Low-Coherence Interferometry and Optical Coherence Tomography for Image-Guided Surgical Treatment of Solid Tumors

ABSTRACT

A system for providing intraoperative feedback to a user during the course of surgery. A core imaging unit provides low-coherence optical radiation coupled to a sampling device and generates optical coherence tomography (OCT) data based on combining scattered light received from the sampling device together with a reference signal. The sampling device is adapted to receive the low-coherence optical radiation from the core imaging unit and to illuminate the tissue, and to collect light scattered by the tissue and to return said light to the core imaging unit. A core software unit receives the OCT data from the core imaging unit provides real-time feedback, such as an image, to the user.

FEDERALLY SPONSORED RESEARCH OR DEVELOPMENT

The subject matter of this application may have been funded in part under a research grants from the National Institutes of Health, under Contract Number 1 R01 EB005221, The Grainger Foundation, and The Carle Foundation. The U.S. Government may have rights in this invention.

BACKGROUND

Optical coherence tomography (OCT) is a high-resolution medical and biological imaging technology. OCT utilizes low-coherence interferometry (LCI) to perform optical ranging within biological tissues. OCT has already previously been demonstrated for being a high resolution real time imaging modality that can provide near-histological information in other clinical applications such as ophthalmology, cardiology, and digestive disease. In use, OCT detects the reflections of low-coherence light, and cross-sectional imaging may be performed by measuring the backscattered intensity of light from structures in tissue. This imaging technique is attractive for medical imaging because it permits the imaging of tissue microstructure in situ. In situ imaging with OCT provides micron-scale imaging resolution without the need for excision and histological processing. OCT has been used in ophthalmology for high-resolution tomographic imaging of the retina and anterior eye. Recently, the technique has been applied for imaging a wide range of nontransparent tissues to investigate applications in tissues studies and medical applications in gastroenterology, urology, and neurosurgery.

OCT measures cross-sectional tomographic images in tissue and is similar to ultrasound B-mode imaging except that it uses light waves rather than sound. OCT also differs from ultrasound in that the detection in OCT is based on interferometry. In ultrasound, the time the ultrasound pulse takes to travel to a surface and be reflected back can be measured by an electronic clock. However, this is not possible with optical techniques because of the high speeds associated with the propagation of light. This limitation is overcome with the use of a reference light path and interferometry. A detailed presentation of the principles of operation of OCT and factors that govern its performance have been previously published. (See Huang D, Swanson, Lin C P, Schuman J S, Stinson W G, Chang W, Hee M R, Flotte T, Gregory K, Puliafito C A, Fujimot J G. Optical coherence tomography. Science. 1991:254:1178-1181; and Swanson E A, Izatt J, Hee M R, Huang D, Lin C P, Schuman J S, Puliafito C A, Fujimoto J G. In vivo retinal imaging by optical coherence tomography. Optics Lett. 1993; 18:1864-1866; both of which are herein incorporated by reference.)

OCT systems may use fiber optics and a compact diode light source similar to those used in compact disc players. Precision distance measurements may be performed by Michelson-type interferometry. In this case, light from the source is split by an optical fiber splitter, which functions as an interferometer. One of the fibers directs light to the tissue and the other to a moving reference mirror, in the case of time-domain OCT. The distal end of the optical fiber can be interfaced to a catheter. In time-domain OCT, the position of the reference mirror is precisely controlled by the system electronics. The light signal reflected from the tissue is recombined with the signal reflected from the mirror. Interference between the light reflected from the tissue and the light reflected from the reference mirror occurs only when the two path lengths are matched to within the coherence length of the light source. This allows precise (micron scale) determination of the distance within the sample from which the light was reflected.

OCT therefore measures the intensity of backscattered (reflected) light from within the tissue, plotted as a function of depth. A cross-sectional image is produced in a manner similar to radar by recording axial reflectance profiles while the transverse position of the optical beam on the tissue specimen is scanned. The image is displayed either in gray scale or false color in order to differentiate tissue microstructure.

Spectroscopic optical coherence tomography (SOCT) is an extension of OCT that can differentiate between different types of tissue. In addition to the normal OCT measurement of the intensity of light backscattered from the sample, SOCT measures the spectral absorption and scattering data from the tissue. Tissue structure can be resolved based on local optical densities, ignoring the frequency dependent changes. SOCT resolves both the amplitude, which contains the scattering and refractive of index information, and the frequency, which contains spectroscopic molecular composition information based on the absorption and scattering properties.

Contrast agents may be used to improve the specificity and targeted tissue visualization of images obtained from an imaging technique, including OCT. Conventional contrast agents serve to increase the intensity of backscattered light. For example, air-filled micro-bubbles and engineering microspheres may be introduced into tissue to increase the backscattering from tissue. In another example, a molecular contrast agent can be used in a pump-probe technique to change the absorption properties of the light.

Currently, it is difficult for surgeons to differentiate between normal and tumor tissue, for example at tumor margins, at the cellular level. Tumor margins may include a tumor mass, which is a mass of abnormal cells, or tumor cells, which are abnormal cells, without a tumor mass. Tumor margins may also include both a tumor mass and tumor cells, which may or may not surround the tumor mass. Tumor margins are classified as either positive—meaning diseased or cancer cells are found on or near the surface of the excised tissue specimen, close—meaning diseased or cancer cells are found within a few mm of the surface, or negative—meaning no diseased or cancer cells are found. These dimensions are the most commonly used dimensions and serve as guidelines in the definition of positive, close, or negative margins. Once the tissue specimen is excised, it is then typically sent to a radiology department for imaging using plain-film X-rays in order to receive a gross confirmation of a wide enough clean margin around the lesion, particularly if metal localization wires or beads were placed in or near the tumor site prior to surgery. The gold standard is to send the tissue specimen to the pathology department where the pathologists will first perform a gross examination of the margin and subsequently evaluate stained tissue sections using light microscopy to view them. Although these are the most common methods used by surgeons to determine whether enough tissue has been removed from the patient during a procedure such as surgery, all diagnostic decisions on a positive, close, or negative tumor margins rely on traditional haematoxylin and eosin, or immunohistochemical staining of a paraffin embedded specimen and evaluation by a pathologist, which can take from hours to days, to determine the presence of cancer cells.

With an increased number of cases as a result of earlier detection or screening of cancer, tumors have become smaller, frequently are non-palpable, and often have unclear demarcations delineating tumor tissue from normal tissue. Therefore, without a real-time in vivo method for microscopic analysis of the tumor margin, surgeons must rely on their own judgment for taking a wide enough margin of normal tissue around a tumor to ensure a negative margin, or wait until the radiology department and/or the pathology department weighs in on the status of the tumor margin.

The current rate of positive margins following solid tumor resection can be significantly high. Research studies have found that the positive-margin rate for breast lumpectomy specimens is as high 64% following the first resection, and fall to only 21% after the third resection. If positive margins are identified while the patient is still in surgery, additional tissue may be taken out. However, if the positive margins are not identified until the final pathological assessment (which often takes at least 24-48 hours post-surgery), the patient will have to return to the hospital for a second surgical procedure to remove additional tissue.

Prior to surgical resection, a tissue specimen is often needed to make a pathological diagnosis and direct treatment options. To obtain tissue, needle-biopsy procedures are frequently performed where a needle is inserted transcutaneously and passed to the site of the suspected tumor mass. Often, an external imaging system is used to facilitate placement of the needle, such as X-ray stereotactic localization, X-ray CT, MRI, or ultrasound. The reliance on these imaging modalities has increased as the number of smaller, non-palpable lesions or masses has increased.

Guiding the tip of the biopsy needle (frequently <1 mm in size) to the correct location at the site of an abnormal lesion (frequently <1 cm) or mass is highly problematic due to lack of operator experience, patient body habitus, mass location, and the imaging field-of-view provided by the external imaging system. Additionally, the lack of being able to localize the lesion in a third dimension of view makes it difficult to find the lesion. Having an evaluation technique at the end of the biopsy needle would prove to be highly useful. Frequently, non-diagnostic samples are obtained from needle-biopsy procedures, which implies that despite an abnormal finding on imaging or exam, only normal tissue is extracted in the needle-biopsy. The non-diagnostic sampling rates can be quite high. For breast masses less than 1 cm in size, the rate is approximately 10-20%. For lung nodules less than 1 cm in size, the rate is as high as 50%. Subsequently, patients require more invasive and extensive open surgical procedures in order to resect the suspicious mass and obtain a diagnosis.

It would be highly desirable to shift the high-resolution microscopic analysis of tumor specimens out of the remote pathology lab and to the point-of-care, or in vivo, where diagnosis and treatment decisions can be made in real-time.

Surgeons do not currently have a standard, reliable, method for assessing lymph nodes interoperatively to determine if they are tumor-bearing. Lymph nodes are the major points of drainage for foreign particles introduced into the human body. Cancer cells that have migrated away from the primary tumor are drained into not only the blood circulation, but also into the lymphatic system and into the lymph nodes. At these sites, the body produces an immune response to combat the cancer cells. This initial interaction produces a reactive lymph node. However, as the cancer cells become more virulent and outgrow or outpace the immune response, they could potentially travel to other organ systems via the lymphatic system and establish secondary or metastatic tumors. Prior to this latter stage, the lymph node is deemed a tumor-bearing node and is often an earlier sign of the potential formation of a metastatic tumor. Currently, it is often necessary to remove a lymph node and evaluate the stained sections under light microscopy in order to determine if the lymph node is tumor-bearing. However, in doing so, pathologists take step-wise sections through the lymph node and prepare these for white-light microscopy assessment. This sectioning protocol will only examine approximately 5% of the entire lymph node, missing a large percentage of the node.

It would be desirable to perform real-time in vivo assessment of a lymph node prior to its resection. This would lead to a reduced number of non-diagnostic lymph nodes being removed and reduced associated complications such as lymphedema, which is the accumulation of lymph fluid at the affected site due to the disruption of the lymphatic network by the removal of lymph nodes.

A number of laboratories have worked toward the detection of cancer, such as breast cancer, using endogenous, or native, optical contrast. Many of the techniques used to exploit this contrast rely upon differences in the spectroscopic response of tissue. Raman spectroscopy, for example, is a nonlinear process that can be used to identify optical signatures due to the chemical composition of tissue. Studies have shown that this technique is effective at distinguishing between normal and diseased tissue in surgical specimens. Similarly, spectral attenuation signatures are well known to vary between healthy and diseased tissue, but these measurements are generally used for evaluation of the intact breast. These techniques have some issues. First, they are not based on the structural properties of the tissue, but rather the chemical signatures, which do not provide information overlayed on the tissue structure, making it harder to localize the tumor or the abnormal tissue depth wise. Second, they are not imaging modalities, per se; they often provide data at a single probing point, not over a region. Third, they do not provide enough cross-sectional depth-wise imaging. Fourth, they are not real-time modalities, but generally require long acquisition time in order to generate sufficient signal for analysis.

Fluorescence-base techniques have also been investigated for the detection of cancer. These methods make use of dyes that are often administered intravenously or topically to the surgical tumor site. The dyes aggregate in the region of the tumor, and the targeted tissue fluoresces when illuminated with an appropriate light source. This technique yields good detection over a large area and could potentially be augmented with microscopic equipment in the operating room. However, these techniques require the use of drug/probe administration, and are limited to surface viewing. Additionally, this method is not suitable for needle-biopsy guidance.

Frozen-section histology has also been used for the detection of cancer during surgical procedures. The problems with frozen-section histology include that it is very time consuming, often yields poor quality results, and usually post-operative histology is still performed. Touch-prep cytology has also been tried for cancer detection. Touch-prep cytology requires a tumor mass margin to be touched to microscope slides and then these slides are viewed under a microscope for tumor cells.

Real-time PCR is another method for detection of cancer. The problem with real-time PCR is that it destroys the tissue sample in an effort to detect abnormal DNA or tumor-identifying material. Various targeted agents and dyes applied topically or intravenously have also been tried for cancer detection. The problem with theses targeted agents and dyes is that they require administration to the patient, either before or during the procedure, their targeting (localization) to diseased cells or tumors is often insensitive and/or non-specific, and the optical systems used to detect these agents lack a high enough magnification and resolution to be able to detect all of the cancer, and individual cancer cells. These agents and dyes are also only viewed at the surface of the tissue, not below the surface.

SUMMARY

In one aspect, the invention provides a method of forming an image of tissue. The method includes beginning an invasive procedure on a patient exposing tissue and acquiring OCT data from the exposed tissue. The method further includes converting the OCT data into at least one image and ending the invasive procedure after the converting of the data.

In another aspect, the invention provides a system for imaging tissue in real-time. The system includes a core imaging unit which generates a low-coherence interferometry signal and a device which is in communication with and receives the low-coherence interferometry signal from the core imaging unit and sends a second signal back to the core imaging unit. The OCT data is generated by the core imaging unit. The system further includes a core software unit which receives the OCT data and performs further data analysis on the OCT data.

In yet another aspect, the invention provides a method of analyzing tissue. The method includes beginning an invasive procedure on a patient exposing tissue and acquiring OCT data from the exposed tissue. The method also includes analyzing the OCT data and classifying the tissue upon analyzing the OCT data.

The scope of the present invention is defined solely by the appended claims and is not affected by the statements within this summary.

The following definitions are included to provide a clear and consistent understanding of the specification and claims.

The term “tissue” means an aggregate of cells and their intercellular substances. Tissue includes diseased tissue and normal tissue. Diseased tissue includes abnormal cells which may be premalignant or malignant. Diseased tissue includes cancerous tissue. Diseased tissue includes tumor tissue. Tumor tissue includes cancerous and benign tumors. Tumor tissue may include a tumor mass along with residual abnormal cells which surround the mass. The tumor mass is a mass of abnormal cells. Tumor tissue also may include abnormal cells which do not form a mass.

The term “tissue margins” refers to an area of tissue whose boundary includes diseased tissue. Tissue margins may include normal tissue as well as diseased tissue. Tissue margins include tumor margins, which is an area of tissue including tumor tissue. The tissue margin may be both on a resected tissue specimen, as well as in the patient (as in the wall of a cavity where the tissue was resected from. Tissue margins are not only resected specimen margins, but any and all “margins”.

The term “radiation” means electromagnetic radiation, including optical radiation in the visible, infrared, ultraviolet, or other spectral regions.

The term “sample signal” means at least a portion of the radiation that is scattered from, reflected from, and/or transmitted through a sample, including a tissue sample.

The term “optical property”, with respect to tissue or other material, means a characteristic of the material that may be quantified by measuring a change in electromagnetic radiation when impinged upon the material, or an emission of electromagnetic radiation from the material.

The term “optical path” means the path along which electromagnetic radiation propagates.

The term “path length” means the distance between two objects based on optical measurements. The path length through a medium between two objects is dependent on the refractive index of the medium, such that the path length may be different from the physical distance between the two objects.

The term “optically coupled” with respect to two components means that radiation is transmitted from one component to the other component.

The term “distal”, with respect to a device or needle, means a position or direction that would be toward or inside the body of the patient when the device or needle is inserted.

The term “OCT” or “Optical Coherence Tomography” means any type of process which uses low-coherence interferometry (LCI) and includes LCI, TD-OCT, SD-OCT, SOOT, and any other of the vast number of other OCT modalities.

The term “OCT data” or “Optical Coherence Tomography data” means any type of data acquired from a process which uses low-coherence interferometry (LCI) and includes data acquired as a result of using LCI, TD-OCT, SD-OCT, SOCT, and any other of the vast number of other OCT modalities.

The term “real-time” means the live or nearly instant sending and receiving of information, such as sound, text, graphical data, or images. Real-time can also refer to the sending or receiving of information before an event expires. For example, in surgery, a real-time assessment of a tumor consists of the sending of information to a surgeon during the surgery and before then ending of that surgery so that a surgeon can make an assessment before the surgery is over.

The term “invasive” or “invasively” means a procedure that requires inserting an instrument or device into the body either through a cavity, through the skin, or through a biological membrane of a patient. An invasive procedure includes a colonoscopy, an endoscopy, swallowing a pill with an imaging device, and other such types of procedures. An invasive procedure also includes any procedure which requires cutting skin or tissue.

The term “expose” or “exposing” means to bring tissue or cells to be imaged close enough to an OCT device so that OCT data may be collected from that tissue or cells. The term “expose” or “exposing” means to bring tissue or cells to be imaged close enough to an OCT device so that OCT data may be collected from that tissue or cells. For example, the phrase “exposing tissue to an OCT device” means bringing the tissue and the OCT device close enough to each other so that OCT data may be collected from the tissue.

BRIEF DESCRIPTION OF THE DRAWINGS

The invention can be better understood with reference to the following drawings and description. The components in the figures are not necessarily to scale, emphasis instead being placed upon illustrating the principles of the invention.

FIG. 1 depicts a schematic representation of an OCT system for acquiring real-time data in vivo.

FIG. 2A depicts an OCT system for acquiring real-time data in vivo.

FIG. 2B depicts a schematic diagram outlining the optical components and hardware used in an SD-OCT system.

FIG. 2C depicts a fiber based device used in an OCT system for acquiring real-time data in vivo.

FIG. 2D depicts a cross-sectional representation of a device containing a housing, a radiation source, and a refractive index measurement assembly.

FIG. 3A depicts a schematic representation of a device for acquiring OCT data.

FIG. 3B depicts a schematic representation of a device for acquiring OCT data.

FIG. 4 depicts a software graphical user interface used to drive an OCT system.

FIG. 5A depicts a flow diagram of a core software package which interfaces with an OCT engine of an OCT system.

FIG. 5B depicts a flow diagram outlining the basic processes involved in OCT Data Acquisition.

FIG. 5C depicts a flow diagram outlining the basic processes involved in Initial Data Analysis and Display of acquired OCT data.

FIG. 6 depicts a flow diagram outlining the basic processes involved in Further Data Analysis and Display of acquired OCT data.

FIG. 7A depicts an OCT image of normal (negative) margin cells with some microvasculature (identified by the arrows) embedded amongst adipose tissue.

FIG. 7B depicts a corresponding H&E stained histology showing microvasculature embedded (identified by the arrows) in adipose tissue.

FIG. 8A depicts normal H&E staining delineating tumor and surrounding tissue.

FIG. 8B depicts an OCT image delineating a suspicious area.

FIG. 8C depicts an estrogen receptor positive immunohistochemical staining outlining the morphological features of an observed tumor.

FIG. 9A depicts a light microscope image of a needle tip showing an angled cutting surface.

FIG. 9B depicts a light microscope image of a needle tip sealed with optical cement.

FIG. 9C depicts light propagation through the single mode (left) and gradient-index fibers (right), optical cement used to secure the fibers, and a cement-sample interface (arrow) where refractive index measurement is performed.

FIG. 10A depicts axial scan data from human tissue using the 20-gauge OCT needle device, the data is from normal fibrofatty tissue exhibiting a characteristic periodic structure.

FIG. 10B depicts axial scan data from human tissue using the 20-gauge OCT needle device, the data is from palpable tumor tissue (ductal carcinoma) exhibiting a dense scattering profile which is correlated with diseased tissue.

FIG. 11A depicts 3-D OCT image taken with a lab-bench setup of a tissue phantom with a uniform distribution of scatterers. The image shown is a corrected image after an ISAM algorithm is applied to the image, the scatterers that are at the top and bottom of the image (on the edges of the focal volume of the Gaussian beam) have been corrected to more accurately depict the true size and shape of the scatterers.

FIG. 11B depicts a 2-D OCT cross section of the image in FIG. 11A.

FIG. 11C depicts 3-D OCT image taken with a lab-bench setup of a tissue phantom with a uniform distribution of scatterers. The image shown is a non-corrected image where the point scatterers have become blurred rendering them indistinguishable.

FIG. 11D depicts a 2-D OCT cross section of the image in FIG. 11C.

FIG. 12A depicts a 3-D OCT image taken with a lab-bench setup of a normal lymph node in a rat mammary model. FIGS. 12B and 12C depict H&E histology data which shows a clear correlation with features identified under H&E staining such as the capsule, cortex, and medullary sinuses of lymph nodes. These are all features that are readily accessible from the other surface of the lymph node. In the normal lymph nodes, the structures appear to be intact.

FIGS. 13A and 13C depict a 3-D OCT image taken with a lab-bench setup of a human lymph node with metastatic squamous cell carcinoma. From the OCT image, there is a distinct breakdown of the normal morphological structure seen in normal lymph nodes. FIGS. 13B and 13D depict planar H&E histology data which corresponds which the 3-D OCT images shown in FIGS. 13A and 13C.

FIG. 14 depicts a 2-D OCT image taken with a clinical OCT system of a human lymph node that was classified as normal by a board-certified pathologist. As can be observed, the overall structural integrity of the node is maintained with the capsule and cortex in a normal lymph node.

FIG. 15 is an exemplary schematic depiction of an optical coherence tomography system in its time-domain and spectral-domain variants.

FIG. 16( a) is an example of OCT data derived from microparticles embedded in a tissue phantom outside of the focus, while FIG. 16( b) is an ISAM reconstruction of the data.

FIG. 17( a) is a schematic depiction of a full-field OCT system in accordance with a preferred embodiment of the present invention.

FIG. 17( b) depicts an example of a band volume for an instrument, in accordance with the present invention, having a numerical aperture of 0.5 and bandwidth from 0.8k_(max)<k<k_(max).

FIG. 17( c) shows the projection of the simulated data collapsed (summed) along one transverse direction, while FIG. 17( d) is a projection of the computed reconstruction of the scatterers.

FIGS. 18( a)-18(c) show three pairs of en face images of the time-domain data (left side) and the reconstructed volume (right).

FIG. 19( a) compares a volume isosurface plot of the raw data with the reconstructed computed image of FIG. 19( b).

FIG. 20 is a schematic depiction of an interferometric synthetic aperture microscope using spectral detection in accordance with an embodiment of the present invention.

FIG. 21 is a schematic view of an OCT catheter shown in cross-section.

FIG. 22 defines the coordinates used in the description of the OCT catheter.

FIG. 23( a) is simulated OCT for randomly scattered point objects and FIG. 23( b) is a reconstruction of the point sources from the simulated data.

FIG. 24 is a plot depicting full-width-half-maximum transverse point-spread-function (PSF) resolution of simulated point sources situated at different distances from the catheter axis, as a function of focus radius and beam width. The abscissa is the distance from the origin from which the simulated point source is placed. In each part, the number next to each curve is the distance away from the origin the beam was focused. The beam waist for each part is (a) 1.5×, (b) 3×, (c) 4.5×, and (d) 6×.

FIG. 25 is a plot depicting full-width-half-maximum axial resolution of simulated point sources imaged with two different beam widths focused 25 wavelengths from the catheter axis, for various fractional bandwidths of the source. The dotted curve corresponds to a 1.5× beam waist, while the solid curve corresponds to a 5× beam waist.

FIG. 26 shows interferometric data from a tissue phantom consisting of titanium dioxide scatterers suspended in silicone. Planar slices the 3-D unprocessed data (left) and ISAM reconstruction (right) are shown for two en face planes above the focus and one below the focus. Magnified unprocessed sections for three depths are shown in (a) at z=1100 μm, (b) at z=475 μm, and (c) at z=−240 μm, where z=0 μm is the focal plane. Magnified ISAM reconstructions for these corresponding planes are shown in (d), (e), and (f), respectively. The scale bar represents 18 μm.

FIGS. 27( a)-(c) show en face images from human breast tissue. (a) Unprocessed interferometric data and (b) ISAM reconstructions are shown for depths located at z=591 μm (Slice A) and z=643 μm (Slice B), where z=0 μm is the focal plane. (c) The corresponding histological sections are shown for comparison.

FIG. 28 is a flowchart depicting steps in imaging a sample using in accordance with embodiments of the present invention.

FIG. 29( a) depicts the relation between spatial frequencies of the signal space and spatial frequencies in the object space; FIG. 29( b) shows a sampling lattice for selected (β, |Q|) values on a uniform (k, |Q|) grid; and FIG. 29( c) shows a sampling lattice for selected (k, |Q|) values on a uniform (β, |Q|) grid.

FIG. 30 is a data flow chart for ISAM processing, in accordance with embodiments of the present invention.

FIG. 31 is a computational flow chart for memory allocation for successive steps of ISAM processing, in accordance with embodiments of the present invention.

DETAILED DESCRIPTION

The present invention makes use of the discovery that real-time, intra-operative or intra-procedure imaging to guide surgical treatment of solid tumors is possible with LCI and OCT imaging. Using the OCT imaging technique to provide high resolution three-dimensional real-time images to visualize on a microscopic scale provides surgeons with the ability to make a real-time in vivo assessment of 1) how clean the resected surgical margins surrounding a tumor are of cancer cells and 2) the status of the loco-regional lymph nodes (normal, reactive, or tumor-bearing) adjacent to the solid tumor, which has important implications for the staging of the spread of the disease. In addition to collecting OCT images, using single depth-scans obtained from LCI, which are essentially single columns of data many of which would normally be used to form an OCT image, real-time LCI or OCT data can be used to guide the placement of needles during needle-biopsy surgical procedures where initial tissue sampling is required to establish a diagnosis.

The present invention also makes use of the discovery that because OCT or LCI can be performed through small, single optical fibers (125 microns in diameter), it is possible for the OCT or LCI light beam to be passed through a biopsy needle and detect or image the tissue directly at the site where the biopsy needle tip is located. Thus, in this application, OCT can be used to directly image near the biopsy needle to guide the needle to the tissue to be biopsied, rather than relying on an external imaging system which suffers from poor resolution or errors due to orientation and localization of the needle tip. Imaging the exact tissue to be biopsied will likely reduce or eliminate the non-diagnostic sampling rate for these needle-biopsy procedures.

Thus, the present invention makes use of the discovery that OCT can be used as an intra-operative and intra-procedure guidance tool for surgeons, providing them with real-time microscopic assessment of tumor margins, needle-biopsy placement, and the status of lymph nodes. Accordingly, the present invention can improve cancer treatment and diagnosis by increasing the percentage of diagnostic tissue samples removed, reducing the amount of normal and functional tissue removed, and decreasing potential adverse effects from surgery such as the need for a tissue re-excision surgical procedure, the risk of lymphedema, or an increased risk of recurrence of the cancer.

FIG. 1 depicts a schematic representation of an optical coherence tomography (OCT) system 100 for acquiring real-time in vivo data. OCT system 100 is a highly modular system that can interface with various devices to widen its range of potential applications as well as interfacing with newer visualization algorithms and classification methods, as discussed herein. The modular nature of the OCT system 100 allows a user to seamlessly interchange these components adapting the system to a user's particular needs and criteria. OCT system 100 includes a core imaging unit 110 that serves as a central unit which interfaces with two other categories of hardware or software components: devices 120 and a core software unit 130.

As shown in FIGS. 2A and 2B, the core imaging unit 110 interfaces and is in communication with device 120. The core imaging unit 110 generates a broadband optical signal which is then run through the device 120 to a tissue sample 121 which is to be analyzed. The signal is then reflected back from the tissue sample 121, back through the device 120 and then to the core imaging unit 110, upon which the reflected signal is combined with the reference signal to create or “generate” an LCI signal, which is detected using a detector and OCT data is acquired from the reflected signal. The core imaging unit 110 is in communication with the core software unit 130 which is run on a computer 125, as shown in FIG. 2A, and sends the OCT data to the core software unit 130 for image processing and analysis. The core software unit 130 is stored in a computer readable storage medium 129 which is connected with the computer 125. The computer 125 also is connected with a processor 127 which runs the core software unit 130. Upon receiving the OCT data, the core software unit 130 converts the raw OCT data into an OCT image and performs further data analysis on the OCT data in order to enhancing the image and/or to classify tissue seen in the image. Preferably, the core software unit 130 can perform the further data analysis on the OCT data in real-time during a procedure, such as surgery, and display or communicate the results to a user, in order to provide real-time feedback to a user. In this manner, the OCT system 100 can not only image tissue and generate OCT data in real-time, but can also provide a real-time analysis and feedback of the OCT data.

Upon imaging the tissue and classifying the tissue, or enhancing the image of the tissue, a user, such as a surgeon, is then able to make a decision regarding how to proceed. For example, if the tissue is being analyzed to determine if it is cancerous, then the tissue specimen margin may be classified as either negative, close, or positive. Upon receiving this classification information, tissue margins can be determined, either by the OCT system 100 or the user, and then the user is then able to remove the tissue within the tissue margins, which may be classified as close or positive. If the tissue is from a lymph node, the lymph node may be removed if the tissue is classified as tumor-bearing for having cancerous cells. Additionally, if the lymph node tissue is classified as negative for having cancerous cells, the user can leave the lymph node intact. Additionally, the tissue classifications can be used to guide a biopsy needle into the tissue. The tissue classifications can also be used to guide localization wires in near the tissue in order to help a surgeon determine the location of tissue, such as diseased tissue, during a procedure.

Preferably, the OCT system 100 is used during a procedure, such as an invasive procedure in which a patient is having surgery. Preferably, the patient is a living human patient. Preferably, the OCT system 100 uses SD-OCT to improve detection sensitivity, to improve signal, phase, and stability, and to reduce the amount of time required to obtain OCT data allowing for a real-time analysis of a patient's tissue. In addition to using SD-OCT, classification algorithms 180 can be used either alone or in conjunction with SD-OCT in order to reduce the amount of time required to classify the tissue being analyzed with the OCT system 100. In this manner, the OCT system can be used to provide a real-time analysis of the patient's tissue. A real-time analysis allows the user to make more informed decisions, such as whether or no to remove certain tissue, before completing the procedure. This prevents the patient from having to undergo the procedure again, or from having too much tissue removed.

The core imaging unit 110 is an LCI or OCT engine, such as a Michelson- or Mach-Zender-type interferometer with accompanying detection, acquisition, processing, and display components, or such as a 3D SDOCT system manufactured by Bioptigen, Inc. of the Research Triangle Park in North Carolina. FIG. 3A is a schematic representation of a low-coherence interferometry device 200 for analyzing a portion of tissue 290. The device 200 includes a low-coherence laser source 210, a fiber optic assembly 220, a reference assembly 230, a sample assembly 240 and an analyzer 250. The fiber optic assembly 220 includes a beam splitter 226 that divides the radiation between the reference assembly 230 and the sample assembly 240. The reference assembly 230 includes a reference mirror 232, which may be moved toward or away from the fiber optic assembly 220. The sample assembly 240 exposes the tissue to the radiation and obtains a sample signal of the radiation that may be scattered, reflected and/or transmitted by the portion of the tissue that is exposed to the radiation.

At least a portion of the sample assembly 240 of a low-coherence interferometry device 200 may be incorporated into a device that can be inserted into tissue in a patient. The radiation that is reflected from the reference mirror 232 constitutes the reference signal, and the reference signal and sample signal are combined to form an interference signal. The interference signal may be directed to the analyzer 250, or the reference and sample signals may be directed to the analyzer and then combined to form the interference signal. The analyzer 250 may process the signals to measure or display the low-coherence interferogram. The analyzer 250 may also determine the refractive index of the tissue and may optionally determine at least one other optical property of the tissue. The analyzer 250 may provide feedback, such as a visual display of the determined values of any optical properties and/or a signal indicating whether a particular tissue has been identified.

In one example of a low-coherence interferometry device, the low-coherence laser source is a Nd:YVO₄ pumped titanium: sapphire laser that yields radiation having a wavelength range from approximately 650 nm to approximately 900 nm after passing through a non-linear fiber. Dispersion and polarization are matched in the reference and sample assemblies. A precision galvanometer is used to scan a reference mirror, and non-linearities in galvanometer speed are relatively small so that interferometric triggering methods are not used. Special fibers, a 3-dB splitter, lenses, signal filtering, and demodulation are used to support the broad optical and electronic bandwidths. The analyzer collects the interferogram data at multiple reference mirror positions and digitizes the signal with an oversampling ratio of at least 2. For applications involving real time analysis, spectral detection with a CCD detector array or accelerated digitization and processing using a field-programmable gate array (FPGA) may be used.

Some OCT engines currently being used for ongoing breast cancer studies are based on traditional spectral domain optical coherence tomography (SD-OCT) engines. A description of an SD-OCT engine can be found in Nguyen FT, Zysk A M, Chaney E J, Kotynek J G, Oliphant U J, Bellafiore F J, Rowland K M, Johnson P A, Boppart S A, “Intraoperative High-Resolution Identification of Breast Tumor Margins,” Submitted to American Journal of Surgery (2007), and in R. Leitgeb, C. Hitzenberger, and A. Fercher, “Performance of Fourier domain vs. time domain optical coherence tomography,” Opt. Express 11, 889-894 (2003), all of which is hereby incorporated by reference. Some other OCT systems being used for ongoing breast cancer studies are based on spectroscopic optical coherence tomography (SOCT).

Acquiring OCT data includes dividing low-coherence radiation between two paths, the reference path and the sample path. Radiation traveling along the reference path is reflected against a reference mirror and then collected as a reference signal. Radiation traveling along the sample path is reflected against a sample mirror and then into the sample tissue. Any radiation that is scattered back from the tissue sample is reflected against the sample mirror and then collected as a sample signal. The signals are filtered to match the dispersion and polarization and then combined into an interference pattern. The resulting interference pattern corresponds to the signal from a single point within the sample. The depth of this point is determined by the distance between the sample and the light source relative to the distance between the reference mirror and the light source, as constructive interference is maximized for signals having the same path length. Variation of these relative distances provides for signals from points at different depths within the sample. Two-dimensional in-plane translation of the sample signal relative to the sample can provide signals across a particular area of the sample.

A variety of techniques can be used to divide the laser radiation into two signals. For example, the radiation can be intersected by a partially reflective mirror, reflecting a portion of the radiation at an angle and permitting the remainder of the radiation to pass through the mirror. The radiation may also be passed through a fiber optic assembly that is configured to split the incident radiation into two fiber optic paths. Variation of the scan depth can be accomplished by moving the reference mirror and/or the sample along the path of the radiation. Variation of the lateral position of the scan can be accomplished by changing the angle of the sample mirror and/or by moving the sample.

FIG. 3B is a schematic representation of an example of a device 300 for acquiring OCT data from a sample 390. OCT device 300 includes a low coherence laser source 310, a fiber optic assembly 320, a reference assembly 330, a sample assembly 340 and a detector 350. The fiber optic assembly 320 may include a preliminary beam splitter 322 that diverts 10% of the radiation to adjustable attenuator 324 connected to the detector 350. The fiber optic assembly 320 includes a beam splitter 326 that divides the radiation between the reference assembly 330 and the sample assembly 340. The radiation that is reflected from the reference assembly 330 and the sample assembly 340 is directed to the detector 350. Reference assembly 330 includes reference mirror 332, which may be moved toward or away from the fiber optic assembly 320. The reference assembly 330 may include fiber collimator 334, for collection of the radiation reflected from the reference mirror 332, and may include a dispersion matching glass 336 to match the dispersion of the reference signal with the sample signal. The sample assembly 340 includes sample mirror 342, which reflects the radiation to the sample 390 in the sample holder 344. The orientation of the sample mirror 342 may be varied to provide for scanning of the radiation across an area of the sample. In addition to or instead of changes in the orientation of the sample mirror 342, the sample holder 344 may be moved along the length and width of the sample. The sample assembly 340 may include fiber collimator 346, for collection of the radiation reflected from the sample mirror 342, and may include a polarization matching paddle 348 to match the polarization of the sample signal with the reference signal. The detector 350 can perform initial processing of the signal to provide the OCT data. Initial processing may include digitization, noise removal and digital aberration correction.

If the laser source has an ultra-broad spectrum, the signal should be transmitted through free space, since fiber-optic components typically cannot accommodate the extremely broad spectrum. A spectral domain OCT setup may also be used to improve the resolution. For applications involving real time analysis, a real time SD-OCT based on a field-programmable gate array (FPGA) implementation can be used. The SD-OCT sample radiation can be delivered to internal body locations with the use of fiber-optic devices and catheters.

As shown in FIG. 1, since the OCT system 100 is modular, the core imaging unit 110 is able to interface with a variety of devices 120, such as handheld devices 122, free-space optical devices 124, and fiber based devices 126. Having this flexibility allows the OCT system 100 to be adapted for use in a variety of different scenarios. For example, the core imaging unit 110 can interface with a free-space optical device, such as a microscope, to image extracted tissue with microscopic detail, and then the core imaging unit 110 can also interface with a fiber-based device, such as a fiber optic cable inserted through a catheter, in order to image, for example a vascular system. This type of flexibility allows devices 120 to be changed in real-time during surgery in order for the OCT system 100 to image vastly different tissue from a patient.

The modular hand held device 122 is any type of probe or optical instrument that can be grasped by a user's hand and be aimed at tissue on or within a patient. The hand held device 122 includes things such as otoscopes for imaging an ear; ophthalmoscopes for imaging the eye; devices that scan the imaging beam at the tip of a pen-like instrument; and devices which are integrated within surgical scalpels, needles, forceps, or biopsy devices. The modular hand held device 122 can be used during a surgical procedure to obtain images of high resolution three-dimensional volumetric data cubes in various areas along and beneath a surface of resected tissue specimens. Alternatively, depending on the accessibility of the cavity, the hand held device 122 can be used to scan around cavity walls in search of tumors or cancer cells. One advantage to imaging a cavity wall as opposed to a resected tissue specimen is the ability to better localize the potential sites where more tissue needs to be removed as well as determining the amount of tissue needed to be removed.

In addition to the hand held device 122, the core imaging unit 110 can also interface with various types of free-space optical devices 124 that are currently being used by surgeons, such as surgical microscopes, heads-up displays, visual magnification eyewear, and wide-field digital cameras, and other such optical devices. Free-space optical devices 124 include any devices or probes which allow significant free-space light propagation in a sample path, especially near the sample surface. By adding the imaging capabilities of OCT, through the core imaging unit 110, to a free-space optical device 124, such as a light microscope, a user can not only get a bright-field image afforded by light microscopy but can also gain a microscopic view of the tissue not only on the surface, but more importantly a few millimeters underneath the surface of the tissue. By taking a traditional imaging technique used to guide surgeons during surgery, such as a free-space optical device 124, and complimenting it with the high-resolution subsurface imaging capabilities of OCT, the user is provided with a method to image tissue on a macro- and microscopic level on and beneath the surface of the tissue and with information on the type of tissue imaged, e.g. cancerous or non-cancerous. This in turn allows the user to better assess the status of tumor margins and the characteristics of lymph nodes. The high-resolution cross-sectional imaging capabilities that the OCT system 100 provides in real-time allows the user to see subsurface tissue features on the same size scale as a pathologist would in light microscopy evaluation of resected specimens.

In addition to free space optical devices 124, the core imaging unit 110 can also be interfaced with a number of fiber based devices 126. Free space optical devices 124 and fiber based devices 126 can be used to image tumor margins and lymph nodes. The free space optical devices 124 are best used for doing a wide-field survey and analysis. Meanwhile, to image deeper into the specimen or to gain a physical measure of the tumor margin, a fiber based device 126 may be inserted into the tissue specimen until a cancerous mass is detected by OCT. This allows a user to remove a more exact amount of tissue in order to get a negative margin, A negative margin is a tissue margin with no diseased tissue, while a positive margin is a tissue margin with diseased tissue.

Fiber based device 126 is any device which can be used to guide light from a first location to a second location, and includes things such as a fiber optic cable or optical fiber. The fiber based devices 126 are typically at least 125 microns in diameter, which is a typical size for an optical fiber, and are used to gain access to sites that cannot be imaged using bulkier devices such as those based on free space optics. The fiber based devices 126 can be guided down the barrels of needles used to place guidance wires to mark the location of the breast cancer lesion under X-ray stereotactic localization, X-ray CT, MRI, or ultrasound. This provides guidance to a user, such as a surgeon, nurse, medical assistant, or lab technician, to the general location of a tumor or lesion, such as a breast cancer lesion.

Because many traditional imaging techniques only provide two dimensional scans, it is sometimes a challenge in localizing the tumor or lesion along a third dimension. Even though one may have properly localized the needle in one plane, that may not hold true for the orthogonal planes. Therefore, the addition of a real-time OCT imaging system at the tip of these needles provides real-time information which further enhances a user's ability to determine, for example, whether or not a tumor or lesion has been properly localized. Similarly, these fiber based devices 126 can be used to guide the needles in core- or fine-needle biopsies allowing for fewer non-diagnostic biopsy specimen to be removed.

FIG. 2D is a schematic representation of a fiber based device 300 that includes a housing 310, a radiation source 320, and a refractive index measurement assembly 330, See Zysk et al., US Patent Publication 2007/0203404, all of which is hereby incorporated by reference. The housing 310 optionally may be configured as a needle with a piercing point 340 at the distal end 350 of the device. In other configurations, the device may be attached to a needle or to a medical device containing a needle. The width of the device may be, for example, from 400 micrometers to 2.0 mm (27-14 gauge). Preferably the device width is from 450 micrometers to 1.8 mm (26-15 gauge), and more preferably is from 500 to 900 micrometers (25-20 gauge). Preferably the device size is minimized so as to reduce the invasiveness of the analysis procedure. The device 300 may be optically coupled to a low-coherence interferometer device.

The radiation source 320 may include an optical fiber that introduces radiation from an external source. Radiation may be passed from one end of the optical fiber through the fiber and to the exposed end, so that the exposed end is a radiation source in the device. The radiation emitted from the exposed end may then be transmitted along an optical path to the tissue. Typically, optical fibers are made of quartz, glass, or a transparent plastic, such as poly(methyl methacrylate) or polystyrene with a fluoropolymer cladding. Examples of optical fibers include single-mode fibers, multi-mode fibers, photonic-crystal fibers, hollow-core fibers, polarization-maintaining fibers and dual-clad fibers. Typical diameters for optical fibers are from 5 to 1,000 micrometers. The optical fiber may be a single-mode fiber or a multi-mode fiber. Single-mode glass fibers have diameters on the order of 10 micrometers. Multi-mode glass fibers have diameters on the order of 50-100 micrometers. Plastic optical fibers have diameters on the order of 1,000 micrometers.

In one embodiment, the fiber based device 126 is run through a tip 128 of a catheter 132. Preferably, the catheter 132 is a balloon catheter having a balloon 136 attached to an end of the tip 128, as shown in FIG. 2C. Preferably, the balloon 136 is transparent, allowing for the signal generated by the core imaging unit 110 to pass through. The catheter 132 is then inserted in to a cavity 136, such as a tumor cavity or a vasculature. A vasculature would include things such as a vein, an artery, or a capillary. Upon insertion into the cavity 136, the balloon 134 is expanded, as shown in FIG. 2C, in order to enlarge the cavity 136 and provide more detailed imaging of that cavity 136. The fiber based device 126 can the be rotated, as shown by the arrow in FIG. 2C, in order to image around the cavity 134, and the fiber based device 126 can also be pulled back along with the catheter 132, in order to obtain a more complete image of the cavity 134. When imaging a tumor cavity, the balloon 134 would be within the tumor cavity, and facilitate the scanning around the inner surface of the tumor cavity, after a tumor mass resection, for example.

In addition to the devices, the core imaging unit 110 also interfaces with the core software unit 130. Upon generating a low-coherence interferometry first signal which is then run through the device 120 to a tissue sample 121, a second signal is then reflected back from the tissue sample 121, back through the device 120 and then to the core imaging unit 110. The core imaging unit 110 then detects the second signal using a detector and generates data which is acquired from the second signal. The generated data is then sent to the computer 125 for data analysis. The core software unit 130 is stored in a computer readable storage medium 129 which is connected with the computer 125. The computer 125 also is connected with a processor 127 through which the core software unit 130 is run.

Preferably, the core imaging unit 110 interfaces with a device 120 which scans over a wide field, as typical lumpectomy specimens are several cubic centimeters and the typical lymph nodes are in the range of 0.25-1 cm³ in size. With such a high-resolution imaging modality and large scanning area provided by the core imaging unit 110, there is a greater need to quickly process and interpret the data so that OCT images can be viewed and evaluated in real-time before the procedure has ended. If the OCT system is to provide images to a user in real-time while the patient is undergoing surgery, it is necessary to process and interpret the data quickly so a decision can be made. Therefore, the OCT system 100 includes the core software unit 130 which includes algorithms which help to process and interpret the data quickly in order to image large areas and identify the type of tissue being imaged (See Zysk and Boppart, Computational methods for analysis of human breast tumor tissue in optical coherence tomography images, J Biomedical Optics, 11:054015, 2006; and see Ralston T S, Marks D L, Carney P S, Boppart S A. Interferometric synthetic aperture microscopy, Nature Physics, 3:129-134, 2007, all of which are incorporated by reference herein).

Similar to the hardware portion of the OCT system 100, the core software unit 130 is used to drive the core imaging unit 110, collect data from the core imaging unit 110 and convert that data to OCT images, and store the OCT images in the storage medium 129. The core software unit 130 includes various add-on components and other rendering and analytical methods, such as Interferometric Synthetic Aperture Microscopy (ISAM) method to correct for the aberrations due to the shape of the Gaussian beam, which is discussed in further detail in Ralston T S, Marks D L, Carney P S, Boppart S A. Interferometric synthetic aperture microscopy. Nature Physics, 3(2):129-134, 2007, all of which is incorporated by reference herein. ISAM is also further discussed herein. The core software unit 130 also includes classification algorithms 180 based on the scattering profiles of individual axial scan data.

In one embodiment, the core software unit 130 performs ISAM on the OCT data in real-time during a procedure, such as surgery. In this manner, the OCT system 100 can not only image tissue and generate OCT data in real-time, but can also provide a clearer image from the OCT data using ISAM. ISAM can therefore be used to enhance the OCT image in real-time and help guide a user, such as a doctor, during a procedure. In another embodiment, referred to herein as an ISAM guided procedure, ISAM can also be used without OCT in real-time during a procedure to enhance images from data received generated by other imaging techniques. Using ISAM in real-time during a procedure to enhance an image would allow a doctor to see items with the image, such as biofilms, with added clarity.

The core software unit 130 is used to quickly process and interpret the data from the core imaging unit 110 in real-time. The core software unit 130 of the OCT system 100 is can be written using commercially available software such as (National Instruments' LabView, and Mathworks' Matlab), or custom non-commercial software. LabView is primarily used to design the graphical user interface (GUI) and to interface with the various drivers to control the hardware components of the OCT system 100 and likewise to interface with the various processing algorithms written in Matlab or C++ or other packages.

The core software unit 130 is broken down into three main components, a data acquisition unit 140, an initial data analysis and display unit 150, and a further data analysis and display unit 160, as shown in FIG. 5A. Implementations of the core software unit 130, the data acquisition unit 140, the initial data analysis and display unit 150, and the further data analysis and display unit 160 each may include computer readable program code. These algorithms, devices and systems may be implemented together or independently. Such code may be stored on a processor, a memory device or on any other computer readable storage medium. The program code may be encoded in a computer readable electronic or optical signal. The code may be object code or any other code describing or controlling the functionality described in this application. The computer readable storage medium may be a magnetic storage disk such as a floppy disk; an optical disk such as a CD-ROM; semiconductor memory or any other physical object storing program code or associated data. A computer readable medium may include a computer program product including the computer readable program code.

FIGS. 5A, 5B, 5C, and 6 represent a flow chart of an example of a computer program product called the core software unit 130, which includes computer readable program code, for quickly processing and interpreting the data from the core imaging unit 110 in real-time. The core software unit 130 begins at 140 by acquiring data obtained by the core imaging unit 110. The data is then sent for initial data analysis and display at 150 upon which the data is taken and converted into an image. Upon forming an image, the image data is then sent for further data analysis and display at 160.

During the further data analysis and display at 160, the data is analyzed further and run through additional algorithms which are used to analyze the data, such as an ISAM method at 170 or classification algorithms at 180. Upon analysis of the data, the further data analysis and display at 160 then displays or communicates the results of the analysis to a user, in order to provide real-time feedback to a user. The real-time feedback allows the user to get information intra-operatively or before a procedure has ended; allowing the user to perform actions on the patient in response to the real-time feedback during a procedure and before a procedure has ended. The further data analysis and display at 160 can communicate the results of the analysis to a user in a number of ways, such as: visually through such things as a display such as an LCD display, a light such as an LED light, or a moving object, such as a projecting member which moves; physically through tactile feedback such as from a vibrating member; sonically using sounds generated from a speaker or other such device; or even through olfactory or taste sensations.

The further data analysis and display at 160 includes running the data through algorithms in order to analyze the data. In one embodiment, the further data analysis and display at 160 includes running the data through an ISAM method at 170 to correct for the aberrations due to the shape of the Gaussian beam. In one embodiment, the data is run through a set of classification algorithms 180 which look for certain optical properties in the image data and based upon those optical properties, the tissue shown by the image data is classified at 190. In one embodiment, the data is run through both the ISAM method at 170 and the classification algorithms at 180.

FIG. 5B is a flow chart representation of a first portion of the core software unit 130. During operation, upon activating the core software unit 130, the core software unit 130 runs through a system initialization process at 131, wherein the core software unit 130 begins running on the computer hardware. Upon performing the system initialization process at 131, the core software unit 130 begins a data acquisition process at 140 by acquiring data obtained by the core imaging unit 110. First a system check 141 is performed to determine if the hardware is functioning properly. Upon performing the system check 141, a load cubic spline interpolation table is loaded at 142 and a data acquisition sequence is begun at 143. The load cubic spline interpolation table at 142 is a resampling method that is used to correct for the nonlinear optical aberrations along with any dispersion compensation that is not achieved in the hardware between the two arms. Upon initiating a data acquisition sequence at 143, sample scanning is then conducted using a device 120, such as a fiber based device 126. Once scanning is done, data acquisition ceases at 145 and data is then acquired from the detector or device 120 at 146 and the data acquisition process 140 is ended and an initial data analysis and display process is started at 150.

As shown in FIG. 5C, data which is acquired from the data acquisition process 140 is sent to the initial data analysis and display process 150. The initial data analysis and display unit 150 processes the raw data acquired from the core imaging unit 110 into a traditional OCT image including some resampling methods to correct for dispersion and other non-linear optical aberrations. First, a background subtraction is performed on the data in the frequency domain at 151. The background subtraction 151 requires that a background image be taken by blocking the sample arm. In this way, the background image is the image of the reference arm signal (this is essentially a power spectrum without the interference overlaid on top of it), and is what is subtracted from the interference signal collected at the detector. Upon performing a background subtraction at 151, a Fourier Transform is performed on the data in the time domain at 152 and a zero-padding upsampling operation is performed on the data at 153. The zero-padding upsampling operation 153 adds a bunch of zeros in the time-domain data. This process increases the “number” of pixels and shifts the “original” useful data into a regime where the cubic spline interpolation works best. Then an inverse Fourier Transform operation is performed on the data in the frequency domain at 154 and a resampling using cubic spline interpolation is performed on the data in the frequency domain at 155. Finally a Fourier transform is performed on the data in the time domain at 156. The Fourier transform is performed at 156 to correct for nonlinear optical aberrations in the hardware. These aberrations can either be corrected for in the hardware optical components or in the software. Upon performing the initial data analysis and display process 150 on the data, the data is sent to a further data analysis and display process which is started at 160.

As shown in FIG. 6, upon forming an image, the image data is then sent for further data analysis and display at 160 upon which the data is run through an ISAM method at 170 to correct for the aberrations due to the shape of the Gaussian beam. More information on the ISAM method is provided in U.S. patent application Ser. No. 60/819,593 filed on Jul. 10, 2006 entitled Interferometric Synthetic Aperture Microscopy (ISAM) Imaging Algorithm, U.S. patent application Ser. No. 11/775,572 filed on Jul. 10, 2007 entitled Interferometric Synthetic Aperture Microscopy (ISAM) Imaging Algorithm, and PCT application No. PCT/US2007/73146 filed Jul. 10, 2007, all of which are incorporated by reference herein.

Upon running the data through the ISAM method at 170, the data is run through a set of classification algorithms 180 which analyze the data and look for certain optical properties in the image data and based upon those optical properties, the type of tissue being imaged is then classified. For example, tissue being imaged can be classified as cancerous or non-cancerous, based upon the analysis done by the classification algorithms 180. In one embodiment, classification algorithms 180 include the processes illustrated in FIG. 6, however, other processes may be used to classify the data.

The classification algorithms 180 can be programmed to use various optical properties which can be derived from the OCT data, such as the scattering profile periodicity or the scattering profile frequency response, in order to classify tissue. One optical property which can be used is a refractive index measurement which provides a measurement of the pathlength between two objects along an optical path traversed by the radiation. The refractive index of the tissue may be calculated by Equation 1:

n=L/d,  EQ. 1

-   -   where n is the refractive index, L is the physical distance         between two objects, and d is the measured pathlength between         the two objects. The device may also include one or more other         devices for measuring the refractive index or other optical         properties besides the refractive index.

In addition to refractive index, the classification algorithms 180 can be programmed to use other optical properties in order to classify tissue. One example of another optical property is the attenuation coefficient, which is a mathematical parameter governing the change in radiation intensity resulting from propagation through a medium. For a device having a refractive index measurement assembly containing an object, such as a reflective surface or an optical fiber, at a fixed physical distance from the radiation source, the attenuation coefficient may be calculated by Equation 2:

σ=˜ln(I/I _(o))/L,  EQ. 2

where σ is the attenuation coefficient, I is the intensity of the radiation measured at the object in the tissue, I_(o) is the intensity of the radiation at the object in a vacuum, and L is the is the physical distance between the object and the radiation source. The attenuation coefficient may also be calculated using an interferogram generated from radiation at another region within the tissue. See, for example, Faber, D. J. et al., “Quantitative measurement of attenuation coefficients of weakly scattering media using optical coherence tomography”, Optics Express, 12(19), 4353-4365 (2004).

Another example of another optical property is the scattering profile, which is a measure of the intensity of radiation reflected or backscattered from the tissue as a function of depth within the tissue. This may be especially useful to identify boundaries between different types of tissues. The scattering profile is analogous to an optical coherence tomography (OCT) axial-scan, in which the tissue is scanned along the depth dimension (axially) as opposed to an OCT b-scan, which scans in two dimensions (both axially and laterally). See, for example, Fujimoto, J. G. et al., “Optical Coherence Tomography: An Emerging Technology for Biomedical Imaging and Optical Biopsy”, Neoplasia, 2(1-2), 9-25 (2000). See also Zysk, A. M. et al., “Computational methods for analysis of human breast tumor tissue in optical coherence tomography images”, Journal of Biomedical Optics, 11(5), 054015-1 to 054015-7, 2006.

Another example of another optical property is the scattering coefficient, which is a mathematical parameter governing the change in radiation intensity due to scattering as a result of propagation through a medium. See, for example, Levitz, D. et al., “Determination of optical scattering properties of highly-scattering media in optical coherence tomography images”, Optics Express, 12(2), 249-259 (2004).

Another example of another optical property is the anisotropy factor, which is a measure of the angle over which incoming radiation is scattered from a medium. See, for example, Levitz, D. et al., “Determination of optical scattering properties of highly-scattering media in optical coherence tomography images”, Optics Express, 12(2), 249-259 (2004).

Another example of another optical property is the birefringence, which is a physical parameter governing the change in polarization of radiation due to propagation through a medium. See, for example, de Boer, J. F. et al., “Two-dimensional birefringence imaging in biological tissue by polarization-sensitive optical coherence tomography”, Optics Letters, 25(2), 934-936 (1997).

Another example of another optical property is the spectral shift, which is a measure of the change in wavelength of the radiation due to propagation through a medium. See, for example, Morgner, U. et al., “Spectroscopic optical coherence tomography”, Optics Letters, 25(2), 111-113 (2000).

Another example of another optical property is the texture, which is a measure of the local variations in brightness within a region of an image. See, for example, Gossage, K. W., “Texture analysis of optical coherence tomography images: feasibility for tissue classification”, Journal of Biomedical Optics, 8(3), 570-575 (2003).

Further examples of optical properties that may be determined in addition to refractive index include Doppler shifts; phase resolution, including phase-resolved Doppler measurements and phase-resolved spectroscopic measurements; light scattering parameters; and spectroscopic absorption. The optical properties listed above may be used in a variety of combinations with refractive index measurements. The refractive index and one or more other optical properties may be determined continuously; or a single optical property determination may provide a baseline analysis, which is then augmented by the determination of the refractive index and/or one or more other optical properties. Classification algorithms can be developed which utilize any of the optical properties listed above to classify the tissue seen in the image data.

As shown in FIG. 6, in one embodiment, as the data is run through the classification algorithms 180, the data is first normalized at 181 and then a subtract linear fit operation is performed at 182. The linear fit subtraction consists of first fitting OCT scan line data (on a log scale) to a straight line via any number of methods (e.g., a least-squares fitting) and then subtracting that line from the scan line data. Then the data can be run through either one of two techniques used to classify the data: 1) a Fourier domain technique; and 2) a periodicity technique. In one embodiment, the classification algorithms 180 use a Fourier domain technique to analyze and classify the image data received from the initial data analysis and display unit 150, as shown in FIG. 6. Upon having a subtract linear fit operation 182 being performed upon the image data, a Fourier transform is performed on the image data at 183 in order to convert the image data to frequency space. The image data is then compared with known Fourier domain data which was previously generated based on known tissue types at 184, and then classified based upon what tissue type the data most closely matches at 190.

In one embodiment, the classification algorithms 180 use a periodicity technique to analyze and classify the image data received from the initial data analysis and display unit 150, as shown in FIG. 6. Upon having a subtract linear fit operation 182 being performed upon the image data, a detect peak algorithm is run at 185 which analyzes and determines where peaks in the data occur. Then the distance between peaks is measured at 186. The average distance between the peaks is computed at 187 and then the average distance between the peaks is then compared at 188 with known distance data which was previously generated based on known tissue types at 184, and then the data is classified based upon what tissue type the data most closely matches at 190. Other techniques can be used to classify the data. For example, the slope of the line calculated for the linear fit subtraction may be used. Learning algorithms or neural networks could also be used to classify the data.

By using the classification algorithms 180 described above, a user operating the OCT system 100 is able to quickly and accurately identify the type of tissue being imaged, such as cancerous or non-cancerous, in real-time. Such analysis is helpful in identifying tumor margins for cancer cells in breast tissue, lung tissue, colon tissue, prostate tissue, brain tissue, thyroid tissue, liver tissue, kidney tissue, ovary tissue, lymph node tissue, skin tissue and other types of human and animal tissue.

In one embodiment, the OCT system 100, and preferably, device 120, includes an indicator 107 used to indicate to a user the results of core software unit 130, such as what type of tissue had been imaged and other properties of that tissue, such as an image of that tissue. The indicator 107 includes any device which can communicate with a user and includes things such as a speaker, a screen, a light, and a vibrating or moving member. In this manner, the indicator 107 can signal to a user if a diseased tissue is present or absent.

The following examples are provided to illustrate one or more preferred embodiments of the invention. Numerous variations can be made to the following examples that lie within the scope of the invention.

Examples

In a first application of the OCT System 100, tumor margins of excised tissue were imaged in an operating room at Carle Foundation Hospital in Urbana, Ill. Patients scheduled to undergo lumpectomy procedures were identified as potential study subjects and informed consent was obtained. Once a surgeon removed a primary breast lesion and a margin of normal tissue, a tissue specimen was imaged using the OCT system 100 by researchers and inked for further histopathological correlations. After the OCT imaging, the specimen was returned to operating room staff to follow the standard of care by sending the specimen to a radiology or pathology department for further assessment of the tumor margin.

The OCT images shown in FIGS. 7A and 7B are largely made up of adipose cells typical of normal breast tissue. As can be observed from the images shown in FIGS. 7A and 7B and corresponding histology, microvasculature, adipose cells, and their nuclei can be seen with good correlation. These are expected results as surgeons attempt to take a wide margin (approximately 1 cm) of normal tissue around the primary breast lesion in order to get a negative margin while the penetration depth of the OCT system is typically in the range of 2-3 mm.

In addition to normal tissue, there have been cases where a tumor was found to be in close proximity to the surface of excised tissue indicative of a close or positive margin, as shown in FIGS. 8A, 8B, and 8C. OCT images identified a suspicious area surrounded by adipose cells. This area was filled with smaller cells and higher scattering intensity signals. Later confirmed by histology (H&E and immunohistochemistry), the suspicious area was indeed the primary tumor and was stained for estrogen receptor positive (ER+) for further confirmation. In comparing the ER+ image with the OCT image, distinct morphological structures can be observed further validating the potential of the OCT system 100 to visualize the microstructure of solid tumors and surrounding tissue.

In one embodiment, the OCT system 100 is outfitted with a prototype fiber optic needle device 137, as shown in FIGS. 9A, 9B, and 9C. This is one example of using the fiber based devices 126 previously described where the fiber based device 126 lies within a metal barrel 133 with a sharpened tip 135 that serves as a needle. The fiber optic needle device 137 can be used on excised tissue specimen in an operating room by inserting the fiber optic needle device 137 at various depths into the tissue specimen. FIGS. 9A, 9B, and 9C demonstrate the size of the fiber optic needle device 137 and diagram light propagation through the tip 135 of the fiber optic needle device 137.

Up to 10-20% of core-needle breast biopsies yield a non-diagnostic sample and, hence, an inconclusive diagnosis. This problem often results in additional surgical procedures due primarily to the lack of an effective tool to assist clinicians in the real-time guidance of microscopic needle placement in non-palpable lesions. Current techniques rely on external techniques, typically X-ray, ultrasound, or palpation, for guidance of the needle device. In one embodiment, these techniques are augmented by an OCT system 100 that can aid in microscopic positioning of the biopsy needle from tissue data taken at the point of tissue removal.

In another application of the OCT System 100, data was generated by the core imaging unit 110 of the OCT system 100 from an image taken in the operating room at the Carle Foundation Hospital in Urbana, Ill. on freshly excised breast tumor tissue. The raw data was then plotted and graphed as shown in FIGS. 10A and 10B. The data was taken from a patient with a preoperative diagnosis of ductal carcinoma in situ. The reflectance profiles presented in FIG. 10A correlate well with known features of normal fibrofatty tissue. The reflectance profiles presented in FIG. 10B correlate well with known features of highly scattering tumor tissue. As can be seen from FIGS. 10A and 10B, the peaks in FIG. 10A are further apart from each other than the peaks shown in FIG. 10B. Additionally, the attenuation of the signal plotted in FIG. 10A is less than the attenuation of the signal plotted in FIG. 10B. Both of these observations are optical properties that can be programmed into the classification algorithms 180, described above, and be used to classify the tissue as either cancerous or not cancerous, or tumor and non-tumor, for example.

To further support the validity of the classification algorithms 180, the classification algorithms 180 were applied to data collected from breast tumor tissue that was imaged under the lab-bench setup at the Beckman Institute in Urbana, Ill. Using this data with a training data set of only three previous patients, these resulted in a highly accurate classification (See Table 1) with sensitivity and specificity ranges similar to that of X-ray and ultrasound detection, but on a microscopic scale.

TABLE 1 Preliminary Classification Results From 4015 Scan Lines Of Human Ductal Carcinoma Tissue Scan Classified Classified Classified False False Sample Lines As Tumor As Adipose As Stroma Sensitivity Specificity Positive Negative Tumor 1408 1170 189 49 0.83 — — 0.17 Stroma 941 196 244 501 — 0.79 0.21 — Adipose 1666 51 1602 13 — 0.97 0.03 —

In addition to the automated classification algorithms 180, other post-processing methods, such as ISAM, can be employed to further enhance the OCT images, better visualize the tumor margins, or improving the quality of the raw data prior to the application of automated classification methods. By modeling the Gaussian properties of the light beam, using ISAM one can correct for the aberrations in the reconstructed image due to the Gaussian shape of the OCT beam. FIGS. 11C and 11D show an OCT image taken by the OCT system 100 before ISAM correction is applied and FIGS. 11A and 11B show an OCT image taken by the OCT system 100 after ISAM correction is applied. As one can see, the images in FIGS. 11A and 11B show more clarity and less blur than the images in FIGS. 11C and 11D.

In another application of the OCT System 100, lymph nodes were imaged using the OCT system 100. In the laboratory, animal studies have been undertaken to study the morphology of lymph nodes in a rat mammary model. An example of a normal lymph 400 node can be seen in FIGS. 12A, 12B, and 12C. Using the OCT system 100, the normal lymph node 400 was imaged and rendered in 3-D. The lymph node 400 was sectioned and stained using hematoxylin and eosin, identifying clear correlation between the OCT images and the histology slides. Typical features identified include the capsule, cortex, and medullary sinuses. As observed under the OCT images, the overall structural integrity of the lymph node 400 appears intact with clear boundaries between the cortex and the capsule and similarly between the medulla and the cortex of the lymph node.

In addition to imaging lymph nodes in an animal model, human lymph nodes 402 were also imaged using the OCT system 100, as shown in FIGS. 13A, 13B, 13C, and 13D. The images in FIGS. 13A, 13B, 13C, and 13D show a high infiltration of cancer cells into the lymph nodes 402 destroying the structural integrity of the lymph node 402 where the boundaries between the various structural layers of the lymph node 402 (capsule, cortex, medulla) are no longer distinct. Morphological structures can also be clearly identified such as the highlighted blood vessel from the images seen in FIGS. 13A and 13B. The images seen in FIGS. 13C and 13D more clearly identify the necrotic tissue and the breakdown of the lymph node architecture. This particular tissue specimen was a cervical lymph node 402 that was resected from a patient with Stage 4, T4N2b squamous cell carcinoma of the oral cavity.

In one embodiment, the OCT system 100 was used to image lymph nodes in the operating room. These lymph nodes were all from breast cancer patients who were already undergoing surgery to remove their primary tumor as well as the sentinel lymph nodes and possibly additional axillary lymph nodes. Only the sentinel lymph nodes were imaged and are the lymph nodes most susceptible to being infiltrated by cancer cells. The lymph drainage from the breast lesion will first drain into the sentinel lymph node before making its way to subsequent nodes in the chain. Thus far, all of the lymph nodes imaged in the operating room were found to be normal by pathology and FIG. 14 is a representative OCT image of the lymph node. As can be observed, the overall structural integrity of the node is maintained with the capsule and cortex in a normal lymph node.

In conclusion, we have demonstrated a number of examples in which the OCT system 100 can be applied to the field of oncology ranging from the assessment of tumor margins, to the guidance of needle core biopsies, to the assessment of lymph nodes. In addition, the OCT system 100 is being presented as a highly modular system that can interface with various devices to widen its range of potential applications as well as interfacing with newer visualization algorithms and classification methods presented here. By helping surgeons define the tumor margin and classify it in terms of a normal, close, or positive margin in the operating room, it will allow surgeons to gauge in real time whether more tissue needs to be removed. This will not only help decrease the rate of recurrence of the cancer but also help reduce the chances of the cancer to metastasize to other organ systems.

The application of OCT to the imaging of lymph nodes demonstrates identifying between normal and tumor-bearing lymph nodes. The images acquired show good correlation with corresponding histology and pathology reports. A real-time analysis of the status of the lymph nodes will allow the surgeons to preserve the lymphatic drainage system as much as possible, removing only those nodes that are deemed to be tumor-bearing.

Of the patients enrolled in all of our clinical studies beyond those whose lymph nodes were imaged under one study at the Carle Foundation Hospital in Urbana, Ill., approximately 2% of all of the lymph nodes removed (sentinel and axillary) were found to be tumor-bearing and 17% of the sentinel nodes were found to be tumor-bearing. These numbers are comparable to national studies indicating a larger need for the real-time in vivo assessment of lymph nodes in the operating room especially when the incidence of lymphedema following breast cancer surgery is estimated to be 25%. Lastly, up to 10% of the core-needle breast biopsies performed resulted in non-diagnostic samples. With the overall goal of reducing the amount of non-diagnostic tissue removed and increasing the number of cancerous and diagnostic tissue removed, the OCT system is demonstrated in a number of potential applications in the field of oncology as a high resolution and highly versatile imaging modality with microscopic analytical capabilities.

Description of ISAM

The following detailed description may be more fully understood by reference to Ralston et al., Inverse Scattering for Optical Coherence Tomography, J. Opt. Soc. Am. A, vol. 23, pp. 1027-37 (May, 2006), which is appended hereto, and incorporated herein by reference.

FIG. 15 shows an example of an OCT system, designated generally by numeral 500, including options to detect the cross-correlation signal in either the spectral domain or the time domain. This particular OCT system uses a coherent light source 512, such as a neodymium:vanadate (Nd:YVO4) pumped titanium:sapphire laser. In the exemplary embodiment depicted, a center wavelength of 800 nm and an average bandwidth of 100 nm yields an axial resolution of 2 μm in tissue. The beam 514 is launched, via coupling optics 515, into a fiber-optic cable 516 and connected to a pair of fiber-optic beam splitters 518, 520 (Gould Fiber Optics, Inc., Millersville, Md.). The interferometer employs a single-mode 50/50 fiber optic splitter 520 that delivers and couples the signals to and from the sample arm 522 and the galvanometer-based reference arm 524. The 90/10 beam splitter 518 serves the purpose of producing a reference spectrum for source noise reduction in the balanced photodetector. This setup can make use of both the single photodetector and the high-speed dual balanced photodetectors 526 and 528. In the sample arm, interchangeable achromatic lenses 30, from 9 mm to 40 mm, can be used to focus from 10 mW to 30 mW of light down to corresponding spot size (determined by transverse resolution). Polarization paddles 532 in the sample arm are able to change the polarization incident upon the sample to achieve maximum interference.

A time-domain system is characterized by capturing axial scans while a reference arm 524 varies the path length in relation to the sample arm 522. There are several designs of varying the path length in the reference arm. In certain embodiments, reference arms may include a standard spatial domain delay, or a rapid scanning optical delay (RSOD) which employs a spatial Fourier shift to create a delay. Typically, a single or dual-balanced photodetector 36 is used to capture interference data.

A spectral-domain system is characterized by capturing the spectrum of a light source and inferring the spatial axial susceptibility. Susceptibility describes, in theoretical terms, the dielectric properties of a material that give rise to scattering and thus to the representation ordinarily considered to constitute an image. There are several ways to detect the spectrum including employing a frequency swept laser and detection with a single photodetector, or a broadband laser and detection using an imaging grating spectrometer 40 so that all frequencies are detected simultaneously.

In order to elucidate the present invention, a theory of inverse scattering is presented that has been developed for optical coherence tomography (OCT) and that is used to resolve three-dimensional object structure, taking into account the finite beam width and focusing. While the invention is described herein in optical terms, it is to be understood that the invention is not so limited, and that the teachings provided herein are equally applicable to any radiation, whether acoustic or of other particles, massive or otherwise, that may be characterized in terms of wave propagation.

By using the invention, transverse and axial resolution produced by conventional OCT imaging inside the confocal volume can be achieved outside of the confocal volume. Explicitly, experiments show that scatterers can be resolved outside of the confocal volume with resolution comparable to that achievable inside the confocal volume. Numerical simulations and experimental results demonstrate the effectiveness of this technique. When the algorithm is applied to experimentally-acquired OCT data, the transverse and axial resolutions outside of the confocal parameter are improved, extending the apparent confocal parameter range. These results further improve the high-resolution cross-sectional imaging capabilities of OCT.

To illustrate the problem in OCT that is solved with ISAM, a sample is designed and imaged, which clearly shows the effect of the probing beam. A tissue phantom, a collection of titanium dioxide scatterers having a mean diameter of 1 μm suspended in silicone, was imaged with a spectral-domain OCT (SD-OCT) system. FIG. 16( a) displays the OCT data with no beam consideration. The 2D ISAM reconstructed image of an area of 500 μm (transverse) by 1000 μm (axial) is depicted in FIG. 16( b), where the bandwidth is 100 nm, the focal length of the lens is 15 mm, the spot size is 11 μm, and the confocal parameter is 996 μm. The image resolution of point scatterers outside of the confocal region for the original experimental image data is not constant, but for the reconstruction, the resolution is relatively constant along the entire image with only amplitude variations. The interference between the light scattered from a group of adjacent particles (boxed) is evident in the original image (top magnified). Methods in accordance with the present invention properly rephase the signal from scatterers to produce a well-resolved image (bottom magnified).

The sample imaged in FIG. 16 consists of a uniform number of scatterers, yet when looking at the reconstruction the number of scatters outside of the confocal region seems to increase. The 2D equivalent of the algorithm resolves only a perpendicular projection of the 3D data set. The imaging beam has a wider contour outside of the confocal region, and thus the beam is incident upon a larger volume illuminating more scatterers.

ISAM fundamentally relies on the solution of the inverse scattering problem, S=Kη, where K is a linear operator which transforms the collected signal S to the object's spatial susceptibility η. (The dimensionalities of S and η are discussed below.) In some geometries, K can be diagonalized in the Fourier domain producing an efficient algorithm for attaining spatially invariant resolution.

There are many embodiments for ISAM, each of which relies on specific imaging geometries and the various embodiments may advantageously be employed in variations on the instrumentation. Different geometries require somewhat different formulations of the forward and inverse scattering problems. Included here are the solutions for three geometries that are most likely to be useful in practice. The first geometry, for a Gaussian beam with a focus transversely scanned over a plane, is the most often used geometry of OCT when external surfaces are to be imaged. The second geometry, for an azimuthally scanned beam, is typically employed for catheters for imaging internally inside the human body, and may be utilized in applications wherein the beam is delivered to the irradiated sample by a needle, a probe, an endoscope, or a laparoscope. Finally, the full-field geometry is useful when external surfaces are to be imaged and speed of data acquisition is paramount. Other instruments will likely be amenable to be adapted to these geometries, and the ability to perform ISAM is not limited to these geometries. The types of incident fields that we have specifically addressed are focused Gaussian beams and plane waves because they are the most common and readily produced and detected beams used for OCT, however the scope of the present invention is not limited to these types of incident field.

In accordance with embodiments of the present invention, the capabilities of both OCT and OCM are greatly extended by computed imaging and synthetic aperture techniques. Among recently demonstrated advantages is the ability to resolve features in the sample that are outside of the confocal region. A more quantitatively accurate and faithful representation of the sample structure than hitherto available is provided by solution of the inverse scattering problem as applied both to full-field planar OCT/OCM as well as to OCT from an azimuthally-scanned catheter. In either case, and in accordance with preferred embodiments of the invention, the focus may advantageously remain fixed at the surface of the sample, while computed imaging techniques are used to infer the structure inside and outside of the depth-of-field. By applying the invention, the focus need not be scanned through the sample.

As further described below, a forward scattering model is derived which relates the measured data to the object structure. From this model, a solution of the inverse scattering problem is obtained that infers the object structure from the data. The achievable resolution and system bandpass is also derived from this forward model, and application of the method is demonstrated by means of a simulation.

Full-Field Non-Scanned Beam Implementation

By means of the novel methods described herein, computed imaging techniques are employed to reconstruct features that are both inside and outside the focus. Instead of scanning the focus through the sample, the focus is fixed at the surface of the sample, and no relative translation is needed between the objective and the sample. A frequency-swept source can be utilized to provide a new degree of freedom, replacing information lost by fixing the focus, without sacrificing detail outside of the focus. Because the objective and sample can remain fixed relative to each other, no translation hardware is needed which makes placing the objective on a fiber optic or a handheld probe easier. This method may lead to faster and more accurate full-field OCT imaging because data acquisition can be very rapid, requiring only that the two-dimensional interferogram is sampled while the frequency of the source is scanned. By virtue of computational image formation, the need to physically form an image of each plane in the volume, as typically done in full-field OCT, is obviated. As data acquisition speed and computational speed continue to increase, video-rate scanning of three-dimensional volumes may become possible.

In order to provide an understanding of computational image formation in the context of full-field OCT, a physical model for the scattering process is developed, and from this, a relationship between the data and the object structure is derived. Based on this relationship, the inverse scattering problem is solved to infer the sample structure from the data.

Full-field OCT allows an entire plane of scatterers to be ranged simultaneously, which makes it a very rapid way to acquire the structure of a volume. A full-field OCT system that is typical of the current state-of-the-art consists of a Michelson interferometer, again, with a broadband illumination source. Reference and sample beams are derived from the broadband source using a beam splitter. An extended area of the sample is illuminated by a broadband collimated beam through a microscope objective. The objective is focused at the depth of features of interest. A signal is scattered by the sample back through the objective. A reference beam is delayed to return to the beam splitter at the same time the signal scattered from the focus arrives. The reference and signal are superimposed and focused on a focal plane array (such as a charge-coupled device (CCD) sensor) which detects the interference signal. The amplitude of the interference signal corresponds to the reflections of scatterers at the focus plane. By translating the sample through the focus plane, the scatterers at many different depths may be ranged.

While this method can be used to obtain high resolution images for entire volumes of a sample quickly, it has a number of disadvantages. First, the sample and microscope objective must be translated relative to each other, which is relatively slow and requires fine positioning. Second, this method uses time-domain detection that produces a lower signal-to-noise ratio than Fourier-domain, or frequency-swept, OCT.

A full-field OCT system, in accordance with embodiments of the present invention, is now described with reference to FIG. 17( a) and is designated generally by numeral 1100. While system 1100, as shown, is based on a Michelson interferometer, other interferometric configurations such as that of a self-referencing Fizeau design, may be used and are encompassed within the scope of the present invention and of any claims appended hereto. In system 1100, the illumination source is a tunable narrow band laser 1112. It is to be understood that partially coherent sources may also be employed within the scope of the present invention, where their application is consistent with the methods described, and that references herein to a laser may also encompass sources that lack temporal or spatial coherence, or both, unless the particular context dictates otherwise.

Laser 1112 is tuned to wavelengths λ that correspond to spatial frequencies k. Laser 1112 nominally emits a plane wave (or is spatially filtered to produce one). The coherence length of this laser should be at least as twice as long as the total depth of the sample 8 under study, to ensure that fields scattered throughout the entire sample simultaneously interfere with the reference field.

Laser illumination 1113 is split by a beam splitter 1114 into two components. One component 1115 travels to a reference mirror (or delay mirror) 1116, and is reflected back through the beamsplitter 1114 to the output port where the focal plane array 1108 is located. It is to be understood that, most generally, numeral 1108 designates a detector, and that references to detector 1108 as a focal plane array are by way of non-limiting example. The other beam component 1117 is demagnified by a factor UM using a telescope 1118 of magnification M. The purpose of telescope 1118 is to concentrate the illumination onto the sample 8, and then relay a magnified scattered field 1120 to the focal plane array 1108. This telescope consists of two converging lenses: a relay lens 1122 and a microscope objective 1124. The illumination on the sample is a normally incident plane wave 1126. The sample scatters some radiation 1128 backwards through the telescope 1118. The telescope is aligned to afocally and telecentrically image the front surface of the sample to the focal plane array. Sitter et al., Three-dimensional Imaging: a Space-invariant Model for Space Variant Systems, Appl. Opt., vol. 29, pp. 3789-94 (1990) discusses three-dimensional imaging problems, and is incorporated herein by reference.

It is to be noted, significantly, that in a manner distinct from that of standard full-field OCT microscopy, the focus of the objective 1124 may remain fixed, in accordance with the present invention, at the surface of sample 8. For purposes of the following heuristic analysis, it is assumed that telescope 1118 is aberration free and vignetting inside the telescope is negligible. If the telescope is assumed to correct spherical aberration, then there is a finite volume within the sample space for which these assumptions hold. A pupil 1130 is placed at the focus of the illumination beam inside the telescope to spatially filter the backscattered signal so as to enforce a well-defined spatial bandlimit. The response of the telescope is modeled by a space-invariant convolution with a bandwidth determined by the pupil size. At the focal plane array 1108, the reference and sample signals superimpose and interfere, and the intensity of the interference is detected. The intereference signal from detector 1108 is coupled to an Inverse Scattering Solver 1132, the operation of which is now described.

To derive the relationship between the object structure and the data detected on the sensor, a mathematical model of scattering of the illumination field by the object and interferometric detection at the sensor is now described with reference to FIG. 28. For convenience of description, a scalar field is substituted for the electromagnetic field, neglecting polarization effects. The incident field on the sample, provided in step 1140, is given by the expression:

E _(t)(r;k)=A(k)exp(ikz)  (1)

where r is a location within the volume of sample 8, k is the spatial frequency of the illumination, A(k) is the amplitude of the illumination at frequency k, and {circumflex over (z)} is the direction of increasing depth into the sample. For present purposes, it is assumed that the scattering is well-modeled by the weak or first Born scattering approximation, where the scattering by the object is modeled as a source. The susceptibility of the object is given by η(r) such that η(r)=0 for z<0.

The secondary scattered field E_(s)(r′;k) from the object at the plane z=0 is given by the expression

$\begin{matrix} {{E_{s}\left( {r^{\prime};k} \right)} = {\int_{V}\ {{^{3}{{rE}_{i}\left( {r;k} \right)}}{\eta (r)}{\frac{\exp \left( {{ik}{{r^{\prime} - r}}} \right)}{{r^{\prime} - r}}.}}}} & (2) \end{matrix}$

To simplify this relationship, it is useful to define the two-dimensional Fourier transform

${{\overset{\sim}{E}}_{s}\left( {q;k} \right)} = {\int_{z^{\prime} = 0}\ {{^{2}r^{\prime}}{E_{s}\left( {r^{\prime};k} \right)}{\exp \left( {\; {q \cdot r^{\prime}}} \right)}}}$

with q being a transverse spatial frequency such that q·{circumflex over (z)}=0. In terms of q, Eq. (2) is found to be

$\begin{matrix} {{{\overset{\sim}{E}}_{s}\left( {q;k} \right)} = {{A(k)}{\int_{V}\ {{^{3}r}\; {\eta (r)}\exp \left\{ {{\left\lbrack {q \cdot r} \right\rbrack} + {{iz}\left\lbrack {k + {k_{z}(q)}} \right\rbrack}} \right\} {k_{z}(q)}^{- 1}}}}} & (3) \end{matrix}$

where k_(z)(q)=√{square root over (k²−q²)}, and substituting Eq. (1) into Eq. (2). (In accordance with convention, x² designates the square modulus of a vector x.) The three-dimensional Fourier transform is defined such that

${\overset{\sim}{\eta}(Q)} = {\int_{V}\ {{^{3}r}\; {\eta (r)}{{\exp \left( {\; {Q \cdot r}} \right)}.}}}$

It is then found that the right-hand integral can be expressed in terms of {tilde over (η)}(Q):

{tilde over (E)} _(s)(q;k)=A(k)k _(z)(q)⁻¹ {tilde over (η)}{q+{circumflex over (z)}[k+k _(z)(q)]}  (4)

The field E_(f)(r;k) is produced by the propagation of E_(s)(r′;k) through telescope 1118 to focal plane array 1108 (shown in FIG. 17( a)). Because the telescope is assumed to be an aberration-free telescope which afocally and telecentrically images the plane at the sample z=0 to the focal plane array in the plane z=z_(f), its function can be modeled by a simple convolution with a point spread function accounting for the finite bandwidth of the telescope, and a magnification factor given by M. The field at the focal plane array is given by E_(f)(r;k), and the point spread function of the telescope is given by P(r;k). The relationship between E_(f)(r;k) and E_(s)(r′;k) is

E _(f)(r;k)=M ⁻ ∫d ² r′E _(s)(r′;k)P(r/M−r′;k)  (5)

where the factor M⁻ accounts for energy conservation between the two planes.

If we further define the Fourier transforms

${{\overset{\sim}{E}}_{f}\left( {q;k} \right)} = {\int_{z - z_{f}}\ {{^{2}{{rE}_{f}\left( {r;k} \right)}}{\exp \left( {\; {q \cdot r}} \right)}}}$

and the coherent transfer function of the telescope {tilde over (P)}(q;k)=∫d²r P(r;k)exp(iq·r), the convolution of Eq. (5) may be expressed as

{tilde over (E)} _(f)(q;k)=M{tilde over (E)} _(s)(Mq;k){tilde over (P)}(Mq;k)=MA(k){tilde over (P)}(Mq;k)k _(z)(Mq)⁻¹ {tilde over (η)}{Mq+{circumflex over (z)}[k+k _(z)(Mq)]}.  (6)

Eq. (6) specifies a relationship between Fourier components of the field on the focal plane array and those of the object susceptibility.

In accordance with preferred embodiments of the invention, reference mirror 1116 is placed to effect a delay on the reference beam 1145 of τ relative to the total delay required for the beam to travel from the beamsplitter 1114 to the plane z=0 in the sample arm and back. The reference field E_(r)(r; k, τ), relayed to the focal plane array is then given by

E _(r)(r;k,τ)=A(k)exp [iω(k)τ],  (7)

-   -   where ω(k) is a dispersion relation relating the temporal         frequency with the spatial frequency in the sample medium.

For example, if the object medium is free space, then ω(k)=kc, where c is the speed of light in vacuum. The interference intensity I(r; k, τ)=|E_(r)(r; k, τ)+E_(f)(r;k)|² on the focal plane array is then given by

I(r;k,τ)=|A(k)|² +|E _(f)(r;k)|²+2A(k)Re{E _(f)(r;k)exp [−iω(k)τ]}.  (8)

The part of the signal 1142 that is due to interference between the signal and reference beams occurring in step 1141 is defined as the data function D(r;k)=A(k)E_(f)(r;k). The complex D(r;k) can be estimated from measurements of I(r; k, τ). For example, three measurements of I(r; k, τ) such that ωτ=0, π/2, and π may be summed (in step 1147 of FIG. 28) to yield, as an approximation:

$\begin{matrix} {{D\left( {r;k} \right)} = {{\frac{1 - }{4}{I\left( {{r;k},0} \right)}} - {\frac{1 + }{4}{I\left( {{r;k},{\pi \text{/}\omega}} \right)}} + {\frac{}{2}{{I\left( {{r;k},{\pi \text{/}2\; \omega}} \right)}.}}}} & (9) \end{matrix}$

The foregoing method of phase-shifting for interferometry is described, for example, in Hariharan, Optical Interferometry (Academic Press, 2003), which is incorporated herein by reference. Inserting the results of Eq. (6), the Fourier transform of the data function, which is {tilde over (D)}(q;k)=∫d²rD(r;k)exp(iq·r), can be expressed as

{tilde over (D)}(q;k)={tilde over (K)}(q;k){tilde over (η)}{Mq+{circumflex over (z)}[k+k _(z)(Mq)]},  (10)

-   -   where, for convenience, the bandpass function is defined

{tilde over (K)}(q;k)=MA(k)² {tilde over (P)}(Mq;k)k _(z)(Mq)⁻¹.  (11)

Thus, the data are expressed in terms of the 3-D Fourier transform of the sample structure, and, so, the resolution of the reconstruction of the sample structure is space invariant. However, vignetting and aberrations in the telescope limit the volume over which this resolution can be obtained.

To obtain the measurements needed to reconstruct η(r), one must vary both k and τ. In practice, however, it is often slow and inconvenient to adjust both. If one is willing to tolerate some image artifacts, just one of these parameters need be scanned. For simplicity, it is assumed that the pupil function P(r′;k) is real and symmetric, which is often the case (for example, when pupil 1130 is circular), so that {tilde over (P)}(q;k) is likewise real and symmetric.

If mirror 1116 is fixed such that τ=0, then the imaginary component of D(r;k) is not obtainable. If the imaginary part of D(r;k) is assumed to be zero, then due to the Hermitian symmetry of the Fourier transform of real functions {tilde over (D)}(−q,k)={tilde over (D)}(q,k)*. The function {tilde over (η)}(Q) then also has Hermitian symmetry reflected over the axis. The effect is that a conjugate image of the susceptibility is present, reflected across the plane z=0. Because the delay τ=0 corresponds to the plane z=0, as long as the entire sample is contained such that z>0, the conjugate image and the real image do not overlap. In addition, there is an artifact corresponding to the term |E_(f)(r;k)|² in Eq. (8). If the magnitude of the sample signal is small relative to the reference signal, the magnitude of this artifact is also small compared to the real image and can be neglected. This term may also be eliminated by modulating the phase of the reference field and locking in only on the modulation, i.e., by phase-sensitive detection of the interference signal.

If the delay τ is scanned, and the laser emits all frequencies k simultaneously (such as occurs in a mode locked laser or a spontaneous emission source), the signal I_(T)(r;τ) is the sum of the interference patterns over all emitted frequencies:

$\begin{matrix} {{I_{T}\left( {r;\tau} \right)} = {{\frac{1}{2\; \pi}\left\lbrack {\int_{- \infty}^{\infty}\ {{{k\left( \frac{\omega}{k} \right)}}\left( {{{A(k)}}^{2} + {{E_{f}\left( {r;k} \right)}}^{2}} \right)}} \right\rbrack} + {\frac{1}{\pi}{Re}{\left\{ {\int_{- \infty}^{\infty}\ {{{k\left( \frac{\omega}{k} \right)}}{D\left( {r;k} \right)}{\exp \left\lbrack {{- }\; {\omega (k)}\tau} \right\rbrack}}} \right\}.}}}} & (12) \end{matrix}$

The term in square brackets in Eq. (12) is a background intensity that is independent of τ and therefore is easily subtracted to remove its contribution from the measured intensity. Neglecting the background intensity and the slowly-varying Jacobian

$\left( \frac{\omega}{k} \right),$

Eq. (12) relates the real part of the inverse Fourier transform of D(r;k) with respect to k to the total intensity I_(T)(r;τ). To be able to remove the Re{ } operation so that a unique solution for D(r;k) can be found, one equates D(r;−k)=D(r; k)*. Eq. (10) then likewise enforces Hermitian symmetry on η(−Q)=η(Q)*. Therefore in this case the reconstructed susceptibility is assumed to be real-valued.

In this derivation, the focal plane of the objective and the front surface of the sample are assumed to coincide (at z=0). This assumption has simplified the preceding analysis and presentation, but it is not required within the scope of the present invention. If the focus is placed below the sample surface by a distance z0, but the delay produced by the reference still coincides with the delay of the sample surface, the data can be modified to account for the displacement. In particular, the modified data {tilde over (D)}′(q;k) is related to the sampled data {tilde over (D)}(q;k) by:

{tilde over (D)}′(q;k)={tilde over (D)}(q;k)exp {iz ₀ [k−k _(z)(Mq)]}.  (13)

This formula can be found by noting that the field relayed by the telescope is now situated at the plane z=z₀, adding an extra term exp {−iz₀[k+k_(z)(q)]} to the right side of Eq. (3). At the same time, the delay reference mirror must be moved a distance further from the beamsplitter so that the new effective delay corresponds to the front surface of the sample, adding a factor of exp(−2ikz₀) to the right side of Eq. (7) to place the reference delay coincident with the front surface of the sample. Effectively the measured field is computationally propagated at each frequency to the surface of the sample.

Using the mathematical model 1146 developed in the foregoing discussion, a solution to the inverse scattering problem may be derived in step 1143. In general, the solution is ill-posed and so regularization techniques are used to produce a stable solution. Because the forward problem is linear, we derive a linearized inverse based on least-squares error. To do so, we first specify the complete forward operator K such that D=Kη, which relates the data to the object structure

{tilde over (D)}(r;k)=Kη=∫d ³ r′K(r′,r;k)η(r′)  (14)

-   -   where the kernel K(r′,r; k) of the operator K is given by

$\begin{matrix} {{K\left( {r^{\prime},{r;k}} \right)} = {M^{- 1}{A(k)}^{2}{\int{{^{2}r^{''}}\frac{\exp \left( {{ik}{{r^{''} - r}}} \right)}{{r^{''} - r}}{{P\left( {{{r\text{/}M} - r^{''}};k} \right)}.}}}}} & (15) \end{matrix}$

Given this relation between the data and the object, we can define a least-squares solution η⁺(r) for object susceptibility as

$\begin{matrix} {{{n^{+}(r)} - {\underset{\eta}{argmin}{{D - {K\; \eta}}}^{2}}} = {\underset{\eta}{argmin}{\int{{^{2}r^{\prime}}{\int{{k}{{{{\overset{\sim}{D}\left( {r^{\prime}\text{;}k} \right)} - {K\; {\eta (r)}}}}^{2}.}}}}}}} & (16) \end{matrix}$

Expressed in operator notation, the solution to this least squares problem is given by the pseudo inverse η⁺=(K^(†)K)⁻¹K^(†)D where K^(†) is the Hermitian conjugate of K and K^(†)K is assumed to be invertible. It is much simpler to formulate the least-squares problem in the Fourier domain, using the relation of Eqs. (10) and (11). If we instead define the operator K such that D=K{tilde over (η)}. This operator can be used to construct a least squares solution {tilde over (η)}⁺ such that:

$\begin{matrix} {{{\overset{\sim}{n}}^{+}(Q)} = {{\underset{\overset{\sim}{\eta}}{argmin}\left( {{{D - {K\; \overset{\sim}{\eta}}}}^{2} + {\gamma {\overset{\sim}{\eta}}^{2}}} \right)} = {\underset{\overset{\sim}{\eta}}{argmin}\left( {{\int{{^{2}q}{\int{{k}{{{\overset{\sim}{D}\left( {q\text{;}k} \right)} - {{\overset{\sim}{K}\left( {q\text{;}k} \right)}\overset{\sim}{n}\left\{ {{Mq} + {\hat{z}\left\lbrack {k + {k_{z}({Mq})}} \right\rbrack}} \right\}}}}^{2}}}}} + {\gamma {{\overset{\sim}{n}\left\{ {{Mq} + {\hat{z}\left\lbrack {k + {k_{z}({Mq})}} \right\rbrack}} \right\}}}^{2}}} \right)}}} & (17) \end{matrix}$

with {tilde over (K)}(q;k) taken from Eq. (11). A Tikhonov regularization term with regularization constant γ has been added to stabilize the solution and ensure that a unique solution exists. The solution {tilde over (η)}^(†)is given in step 1144 by

$\begin{matrix} {{{\overset{\sim}{n}}^{+}\left\{ {{Mq} + {\hat{z}\left\lbrack {k + {k_{z}({Mq})}} \right\rbrack}} \right\}} = {{\left( {{K^{\dagger}K} + \gamma} \right)^{- 1}K^{\dagger}D} = {\frac{{\overset{\sim}{D}\left( {q\text{;}k} \right)}{{\overset{\sim}{K}}^{*}\left( {q\text{;}k} \right)}}{{{\overset{\sim}{K}\left( {q\text{;}k} \right)}}^{2} + \gamma}.}}} & (18) \end{matrix}$

Resolution and Bandpass of Full-Field ISAM

Eq. (10) expresses a relationship between the 2-D Fourier transform of the data and the 3-D Fourier transform of the object. As mentioned previously, this relationship implies that the resolution of the reconstructed object is space invariant. With suitable specifications of the instrument, it is possible to identify the region of the Fourier space of the structure function that can be sampled. This region is called the “band volume” and is an analogue to the bandlimit of one-dimensional signals, except that the band volume consists of the interior of a shape in three-dimensional Fourier space rather than just a one-dimensional interval.

There are two specifications of the instrument that determine the shape of the band volume. The first is the bandwidth of the illumination, which is specified by the interval of frequencies k_(min)<k<k_(max). The other parameter is the numerical aperture (NA) of the imaging system 0<NA<1. A particular numerical aperture implies a pupil bandpass

{tilde over (P)}(q;k)=1 for |q|≦(NA)k

{tilde over (P)}(q;k)=0 for |q|>(NA)k.  (19)

These inequalities constrain which points on the data function D(q;k) can be sampled. The relation of Eq. (10) is a one-to-one mapping between each of these points in the data function and points in the 3-D Fourier space of the object {tilde over (η)}(Q). The band volume is the intersection of the volumes defined by the two inequalities expressed in terms of the object spatial frequency Q

$\begin{matrix} {k_{\min} < {Q^{2}\text{/}\left( {2{Q \cdot \hat{z}}} \right)} < {{k_{\max}\left( {2{Q \cdot \hat{z}}} \right)}\sqrt{Q^{2} - \left( {Q \cdot \hat{z}} \right)^{2}}\text{/}Q^{2}} < {{NA}.}} & (20) \end{matrix}$

FIG. 17( b) shows an example of a band volume for an instrument with 0.5 NA and bandwidth from 0.8 k_(max)<k<k_(max). The units of the axes are all scaled by k_(max). There are two views so that the top and bottom surfaces are both visible. The top and bottom surfaces are spherical (with different radii and centers), and the side surface is a right circular cone with its vertex at the origin.

In the limit of small bandwidth and low numerical aperture, the band volume shape approaches that of a circular cylinder. In this limit, the resolution in the axial direction is determined solely by the bandwidth, and the transverse resolution is determined by the numerical aperture, as is normally assumed in OCT. However, the band volume becomes less cylindrical and more cone-shaped as the numerical aperture and bandwidth increase, and axial and transverse resolutions are dependent on both the bandwidth and numerical aperture.

Simulation of Full-Field ISAM

A simulation is now presented to demonstrate inverse scattering in full-field OCT. For purposes of the simulation, an object (element 8 shown in FIG. 17( a)) is taken as comprising a set of randomly placed point scatterers. The simulated object was imaged with a simulated full-field OCT system, and then the structure of the object was reconstructed from the data. The simulated object volume cross-sectional area was 25 wavelengths in depth, and 40 by 40 wavelengths in the transverse direction. The illumination source had a Gaussian spectrum with a 40% fractional full-width-half-max bandwidth (corresponding, for example, to 320 nm of bandwidth centered at 800 nm). The simulated numerical aperture of the imaging objective was 0.5.

To synthesize the data, first the scattered field E_(s)(r′;k) was calculated using Eq. (2), where the object η(r) was a collection of randomly chosen discrete points. From this, a two-dimensional Fourier transform computed {tilde over (E)}_(s)(q; k). Then the synthesized data function was calculated by {tilde over (D)}(q;k)=A(k){tilde over (E)}_(s)(q;k){tilde over (P)}(q;k). Finally, a two-dimensional inverse Fourier transform yielded D(r′;k). Eq. (10) was deliberately not used to compute the data because using an alternate and more direct method of computing the data provided a better test of the inverse scattering method.

FIG. 17( c) shows the projection of the simulated data collapsed (summed) along one transverse direction. The units are in terms of the center wavelength. Instead of showing the Fourier-transformed function {tilde over (D)}(r;k) itself, which would be difficult to interpret if it was plotted directly, we show the inverse Fourier transform of {tilde over (D)}(r;k) with respect to k. It is the data on the focal plane array that would be observed if the delay τ were scanned, rather than the frequency k, which is given by the intensity function of Eq. (12). The focus is on the top surface at zero depth, which also corresponds to zero delay. As can be seen, as the delay is increased from zero, the diffracted images of the point scatterers become increasingly large. This corresponds to the standard degradation in resolution one expects from defocus when inverse scattering is not used.

To compute the image estimate η⁺(r) from the synthetic data D(r; k), first {tilde over (D)}(q;k) was computed using the two-dimensional Fourier transform. Next, Eq. (18) was used to compute {tilde over (η)}⁺{q+{circumflex over (z)}[k+k_(z)(q)]}. However, in practice to find n⁺(r) from {tilde over (η)}⁺(Q) numerically, one would likely use the three-dimensional inverse discrete Fourier transform. Unfortunately, Eq. (18) does not specify {tilde over (η)}⁺ in a form to which the inverse discrete Fourier transform can be readily applied, because it is a function of the more complicated argument q+{circumflex over (z)}[k+k_(z)(q)]. In practice, this means that the discrete sampling of the function {tilde over (η)}⁺ is uniform in the variables q and k and not in Q to which the inverse Fourier transform can be directly applied. By using an interpolator, one can compute the samples of {tilde over (η)}⁺ on points that are uniform in Q from existing samples of {tilde over (η)}^(†){q+{circumflex over (z)}[k+k_(z)(q)]}. In this simulation, a one-dimensional cubic B-spline interpolator was used to interpolate from the coordinates q+{circumflex over (z)}[k+k_(z)(q)] to Q. Because only the {circumflex over (z)} coordinate is not sampled uniformly, the resampling only needs to occur along this direction.

Finally, after taking the three-dimensional inverse Fourier transform of {tilde over (η)}⁺(Q), the reconstruction {tilde over (η)}⁺(r) results, which is shown in FIG. 17( d). As can be seen, the reconstruction corrects for the diffraction of the data, and produces point-like images. FIG. 18 shows three en face planes corresponding to the depths A, B, and C marked in FIG. 17( c). The left column is the time-domain data measured in each of the en face planes, and the right column is the image of the scatterers computed by inverse scattering. Planes that are further from the focus have more diffuse images when viewed in the raw data because of the effect of defocus. One can also see the interference between the images of adjacent scatterers. Despite the interference between scatterers, each point is clearly resolved with space-invariant resolution in the reconstructed image. This shows the algorithm correctly separates the interference patterns from scatterers to produce high resolution images.

To show the overall improvement to the data, FIG. 19( a) is a volume isosurface plot of the raw data, while the reconstructed computed image is shown in FIG. 19( b). Again, the blurring of the data is increasingly apparent with increasing distance from the focus plane at the top of the volume. In addition, stripe-like features can be seen for the isosurfaces corresponding to interfering scatterers. This method can correct for the diffraction effects and produce point-like images in FIG. 19( b) for each of the scatterers. The planes of the scatterers need not be so widely separated for the algorithm to distinguish them, but was deliberately done to make the diffraction effects easier to visualize.

There is an important difference in the reconstructions of full-field OCT and conventional scanned beam OCT. In conventional scanned beam OCT, it has been shown by Ralston et al., Inverse Scattering for Optical Coherence Tomography, J. Opt. Soc. Am. A, vol. 23, pp. 1027-1037, (2006), incorporated herein by reference, that the magnitude of the signal captured from scatterers away from the focus is inversely proportional to the distance from the focus. In practice this places a limit on the axial range of the sample that can be imaged before the signal-to-noise ratio becomes unacceptable. However, there is no such attenuation of the signal away from the focus in the full-field OCT case. The practical limit to the depth of full-field OCT is determined by vignetting of the relayed field inside the relay telescope, and the scattering of the sample. However, this advantage may be offset because full-field OCT may be less able to discriminate between single scattering and multiply scattered photons due to its multimode detection.

Transverse-Scanned Focused Gaussian Beam Implementation

Preferred embodiments of the present invention implement computed interferometric imaging by employing a fiber-optic Michelson interferometer 600 seeded by a source of femtosecond pulses, as now described with reference to FIG. 20. A spectral interferometer, designated generally by numeral 602, measures the interferometric cross-correlation between a fixed-delay reference pulse and a pulse reflected back from a sample 8. The measured spectrum on a line camera 604 corresponds to the Fourier transform of the cross-correlation signal, from which the amplitude and phase of the reflected field from the sample are inferred. The sample probe beam 606 is focused by a microscope objective 608 so that the beam focus is at a fixed distance inside the sample. At each position of the beam, the spectral interferogram of the backscattered optical field is measured. The beam is laterally translated in two-dimensions through the sample by moving a stage 610 or by steering the beam with a pair of galvanometer-driven mirrors 612 before entering the objective.

Measurements are made using a femtosecond spectral interferometer 600. Fourier-domain, or frequency-swept, OCT, has been described by Choma et al., Sensitivity advantage of swept source and Fourier domain optical coherence tomography, Opt. Expr., vol. 111, pp. 2183-89 (2003), which is incorporated herein by reference. A femtosecond laser 614 (such as supplied by Kapteyn-Murnane Laboratories of Boulder, Colo.) delivers ultrashort pulses to provide broadband illumination for the system. In one embodiment of the invention, the center wavelength of the source is 800 nm, with a bandwidth of 100 nm. These first-order field quantities fluctuate too rapidly to be detected directly, thus an optical fiber-based Michelson interferometer is incorporated. The illumination is divided by a 50:50 fiber-optic coupler (splitter) 616 between a reference arm 618 containing a delay mirror 620 and a sample arm that contains a lens (objective) 622 to focus the Gaussian beam into the sample 8. Light returns from the sample and reference arms and is directed into spectrometer 602. In the spectrometer, the light is collimated with an achromatic lens 624 and dispersed off of a blazed gold diffraction grating 626, which, in one embodiment, has 830.3 grooves per millimeter and a blaze angle of 19.70 degrees for a blaze wavelength of 828 nm. To reduce lens aberrations, the dispersed optical spectrum is focused using a pair of achromatic lenses 628. The focused light is incident upon a line-scan camera (L104k-2k, Basler, Inc.) 604 which contains a 2048-element charge-coupled device (CCD) array with 10×10 μm detection elements. Camera 604 operates at a maximum readout rate of over 29 kHz, thus one axial scan can be captured during an exposure interval of about 34 μs. The data is sent to processor 630 which may also govern operation of a galvanometric controller 642 and receive a trigger derived therefrom in order to activate frame acquisition, for example.

We obtain a mathematical model of interferometric synthetic aperture microscopy (ISAM) by considering the propagation of the focused beam from the objective into the sample (into some volume V), scattering within the sample (in the first Born approximation), the propagation of the scattered light back into the objective (over some surface Σ), and the measurement of the cross-correlation with the reference pulse. The expression that models these steps (17) is given by

S(r ₀ ,k)=A(k)∫_(Σ) d ² r∫ _(V) d ³ r′G(r′,r,k)g(r′−r ₀ ,k)η(r′)g(r−r ₀ ,k)  (21)

where k is the wave number of the illumination, r₀ is the transverse position of the Gaussian beam, g describes the normalized Gaussian beam profile, A²(k) is the power spectral density of the source, G is the Green function, and η is the susceptibility of the sample. The normalized beam profile is given by g(r,k)=W⁻²(k)e^(−r) ² ^(/2W) ² ^((k))/2π, where W(k)=α/k, α=π/NA, and NA is the numerical aperture of the beam. The Green function is given by G(r′, r, k)=e^(ik(r−τ′))/|r−e′|. After two-dimensional (2-D) Fourier transformation with respect to r₀, and further manipulation, the 2-D Fourier transform of the signal is given by the expression

$\begin{matrix} {{{\overset{\sim}{S}\left( {Q,k} \right)} = {{A(k)}{\int{{^{2}q}{\int{{z^{\prime}}\frac{2\pi}{k_{z}(q)}^{\; {k_{z}{(q)}}{({z^{\prime} - z_{0}})}}{{\overset{\sim}{g}}_{0}\left( {q,k} \right)}^{\; {k_{z}{({Q - q})}}{({z^{\prime} - z_{0}})}}{{\overset{\sim}{g}}_{0}\left( {{Q - q},k} \right)}{\overset{\sim}{n}\left( {Q\text{;}z^{\prime}} \right)}}}}}}},} & (22) \end{matrix}$

where k_(z)(q)=√{square root over (k²−q²)}, z₀ is the position of the beam focus, {tilde over (η)}(Q, z¹) is the 2-D transverse Fourier transform of the susceptibility, and {tilde over (g)}₀(q,k)=e^(−q) ² ^(α) ² ^(/2k) ² is the 2-D Fourier transform for the beam profile g(r,k) in the waist plane of the beam. After the expression for {tilde over (g)}₀ is substituted into Eq. (22), and an asymptotic expansion of {tilde over (S)} is made for large α², this relationship reduces to

$\begin{matrix} {{{\overset{\sim}{S}\left( {Q,k} \right)} = {{A(k)}\left( {\frac{{2\pi}^{2}}{k_{z}\left( {Q\text{/}2} \right)}\frac{k^{2}}{\alpha^{2}}^{{- 2}\; {k_{z}{({Q\text{/}2})}}z_{0}}^{- \frac{\alpha^{2}Q^{2}}{4k^{2}}}} \right){\overset{\approx}{n}\left( {{Q\text{;}} - {2{k_{z}\left( {Q\text{/}2} \right)}}} \right)}}},} & (23) \end{matrix}$

where {tilde over ({tilde over (η)} is the 3-D Fourier transform of η, i.e. the one dimensional Fourier transform of {tilde over (η)}(Q;z) with respect to z. This expansion is valid even when NA≈1 because α² is sufficiently large for the first term of the expansion to dominate. Eq. (23) relates the 3-D Fourier transform of the object susceptibility to the 2-D Fourier transform of the signal. Implicit in this formula is a diagonal linear integral operator in the 3-D Fourier space of the susceptibility, and so the achievable resolution is spatially-invariant and does not depend on the proximity to the focus.

Because of the simple relationship between the susceptibility and the signal, ISAM can be implemented efficiently by resampling or interpolating the data in a manner analogous to the numerical implementation of the Fourier projection slice theorem, as described in Natterer, The Radon Transform, (Wiley, 1986, incorporated herein by reference) and as used in x-ray computed tomography or synthetic aperture radar (SAR), but the resampling grid for ISAM is hyperbolic rather than polar. In addition, since Eq. (23) is a multiplicative (or diagonal) form, generalization to a regularized inverse method such as Tikhonov regularization (Tikhonov, Dokl. Akad. Nauk S S R, vol. 39, p. 195, 1943) is straightforward.

Regardless of the type of detection used, the beam orientation is fixed while the axis is translated over the sample on a Cartesian grid in directions orthogonal to the beam axis and subsequent axial scans are displayed on adjacent lines to form a tomogram. Suppose the beam is generated by light emerging from an optical fiber and then propagating through a lens to form a focused beam incident on the sample. With the axis of the fiber passing through the point r₀ in the z=0 plane and with the waist plane of the focused field at z=z₀, the incident field may be described by the power spectrum |A(k)|² and a normalized mode g such that

U _(i)(r,r ₀ ,k)=A(k)g(r−r ₀).  (24)

The beam may be described in a plane wave decomposition,

$\begin{matrix} {{{g\left( {{r - r_{0}},k} \right)} = {\frac{1}{\left( {2\pi} \right)^{2}}{\int{{^{2}q}\; ^{\; {q \cdot {({r - r_{0}})}}}^{\; {k_{z}{(q)}}{({z - z_{0}})}}{{\overset{\sim}{g}}_{0}\left( {q,k} \right)}}}}},} & (25) \end{matrix}$

where {tilde over (g)}₀ is the two dimensional Fourier transform of g in the z=z₀ plane, and the dispersion relation is given by k_(z)=√{square root over (k²−q²)}. The beam waist is assumed to depend on the wave number, as W₀(k)=α/k where α=π/NA and NA is the numerical aperture of the output lens. Thus

{tilde over (g)} ₀(q,k)=e ^(−q) ² ^(W) ⁰ ² ^(/2) =e ^(−q) ² ^(α) ² ^(/(2k) ² ⁾.  (26)

The scattered field, within the first Born approximation, is given by

U _(s)(r,r ₀ ,k)=∫d ³ r′G(r′,r,k)U _(i)(r′,r ₀ ,k)η(r′).  (27)

Making use of the expressions above for the incident field,

U _(s)(r,r ₀ ,k)=A(k)∫d ³ r′G(r′,r,k)g(r′−r ₀ ,k)η(r′).  (28)

The signal coupled back in to the fiber is given by the projection of the backscattered field onto the fiber mode g at the exit plane of the fiber. Thus

S(r ₀ ,k)=∫_(z=0) d ² rU(r,r ₀ ,k)g(r−r ₀ ,k),  (29)

which becomes

S(r ₀ ,k)=A(k)∫_(z=0) d ² r∫d ³ r′G(r′,r,k)g(r′−r ₀ ,k)g(r−r ₀ ,k)η(r′).  (30)

The Green function for free-space is given by the angular spectrum

$\begin{matrix} {{{G\left( {r^{\prime},r,k} \right)} = {\frac{}{2\pi}{\int{{^{2}q}\; ^{\; {q \cdot {({r - r^{\prime}})}}}\frac{^{{- }\; {k_{z}{(q)}}{({z - z^{\prime}})}}}{k_{z}(q)}}}}},} & (31) \end{matrix}$

where it is assumed that the scatterers are all located such that z<z′ for the whole support of the scatterers. Making use of this expression and Eq. (30), it may be seen that the two-dimensional Fourier transform of S with respect to r₀ is given by the expression

$\begin{matrix} {{\overset{\sim}{S}\left( {Q,k} \right)} = {{2\pi}\; {A(k)}{\int{{^{2}q}\; {\int{{z^{\prime}}\frac{1}{k_{z}(q)}^{\; {k_{z}{(q)}}{({z^{\prime} - z_{0}})}}^{\; {k_{z}{({q - Q})}}{({z^{\prime} - z_{0}})}}^{\frac{{- \alpha^{2}}q^{2}}{2k^{2}}}^{\frac{{- \alpha^{2}}{{q - Q}}^{2}}{2k^{2}}}{{\overset{\sim}{n}\left( {Q,z^{\prime}} \right)}.}}}}}}} & (32) \end{matrix}$

This equation may be solved for η by blunt numerical methods. Such methods are numerically expensive. An analytic result may be obtained by considering the shifted form of the integral

$\begin{matrix} {{\overset{\sim}{S}\left( {Q,k} \right)} = {{2\pi}\; {A(k)}{\int{{^{2}q}\; {\int{{z^{\prime}}\frac{1}{k_{z}(q)}^{\; {k_{z}{(q)}}{({z^{\prime} - z_{0}})}}^{\; {k_{z}{({q - Q})}}{({z^{\prime} - z_{0}})}}^{\frac{{- \alpha^{2}}q^{2}}{4k^{2}}}^{\frac{{- \alpha^{2}}{{q - {Q\text{/}2}}}^{2}}{k^{2}}}{{\overset{\sim}{n}\left( {Q,z^{\prime}} \right)}.}}}}}}} & (33) \end{matrix}$

For large values of α this integral may be evaluated asymptotically. The integrand, modulo the Gaussian, may be expanded in a Taylor series around the point q=Q/2,

$\begin{matrix} {\frac{^{{\;\lbrack{{k_{z}{(q)}} + {k_{z}{({q - {Q\text{/}2}})}}}\rbrack}{({z_{0} - z^{\prime}})}}}{k_{z}(q)} = {{\frac{^{2\; {k_{z}{({Q\text{/}2})}}{({z^{\prime} - z_{0}})}}}{k_{z}\left( {Q\text{/}2} \right)} + {{q \cdot \bigtriangledown_{q}}\frac{^{{\;\lbrack{{k_{z}{(q)}} + {k_{z}{({q - {Q\text{/}2}})}}}\rbrack}{({z_{0} - z^{\prime}})}}}{k_{z}(q)}}}_{q = {Q\text{/}2}}{+ \ldots}}} & (34) \end{matrix}$

Replacing this part of the integrand, the leading term is given by an integral over the constant term in the Taylor expansion:

$\begin{matrix} {{\overset{\sim}{S}\left( {Q,k} \right)} = {{2\pi}\; {A(k)}^{\frac{{- \alpha^{2}}q^{2}}{4k^{2}}}{\int{{z^{\prime}}\frac{^{2\; {k_{z}{({Q\text{/}2})}}{({z^{\prime} - z_{0}})}}}{k_{z}\left( {Q\text{/}2} \right)}{\int{{^{2}q}\; ^{\frac{{- \alpha^{2}}{{q - {Q\text{/}2}}}^{2}}{k^{2}}}{{\overset{\sim}{n}\left( {Q,z^{\prime}} \right)}.}}}}}}} & (35) \end{matrix}$

The Gaussian integral may be easily carried out and the remaining integral is seen to be a Fourier transform with respect to z′,

$\begin{matrix} {{{\overset{\sim}{S}\left( {Q,k} \right)} = {\frac{k^{2}}{\alpha^{2}}{{2\pi}\;}^{2}{A(k)}\frac{^{{- 2}\; {k_{z}{({Q\text{/}2})}}z_{0}}}{k_{z}\left( {Q\text{/}2} \right)}^{\frac{{- \alpha^{2}}q^{2}}{4k^{2}}}{\overset{\approx}{n}\left\lbrack {Q,{{- 2}{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack}}},} & (36) \end{matrix}$

where {tilde over ({tilde over (η)} is the three-dimensional Fourier transform of η. The next term in the expansion yields a contribution proportional to α⁻⁴. In the extreme limit that NA→1, it may be seen that α→π so that we expect the leading term approximation to be sufficient even in the case of high numerical aperture. It might be noted that this expansion is distinct from the paraxial approximation (essentially a small |q| expansion of k_(z)(q)) which fails as NA→1. Eq. (36) expresses a resampling scheme illustrated in FIG. 15. To find an appropriate regularization scheme, we will write

{tilde over (S)}(Q,k)=∫dβH(Q,k,β){tilde over ({tilde over (η)}(Q,β),  (37)

where

$\begin{matrix} {{H\left( {Q,k,\beta} \right)} = {{\frac{k^{2}}{\alpha^{2}}{{2\pi}\;}^{2}{A(k)}\frac{^{{- 2}\; {k_{z}{({Q\text{/}2})}}z_{0}}}{k_{z}\left( {Q\text{/}2} \right)}^{\frac{{- \alpha^{2}}q^{2}}{4k^{2}}}{\delta \left\lbrack {\beta + {2{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack}} \equiv {{f\left( {Q,k,\beta} \right)}{{\delta \left\lbrack {\beta + {2{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack}.}}}} & (38) \end{matrix}$

Then the kernel of the normal operator is given by the expression

$\begin{matrix} {{H^{*}{H\left( {Q,\beta,\beta^{\prime}} \right)}} \equiv {{{f\left( {Q,{1\text{/}2\sqrt{\beta^{2} + Q^{2}}},\beta} \right)}}^{2}\frac{\beta}{2\sqrt{\beta^{2} + Q^{2}}}{{\delta \left( {\beta - \beta^{\prime}} \right)}.}}} & (39) \end{matrix}$

And the kernel of the Tikhonov regularized psuedo-inverse, with white noise N is given by the expression

$\begin{matrix} {{H^{+}\left( {Q,{k;\beta}} \right)} = {\frac{{f^{*}\left( {Q,k,\beta} \right)}{\delta \left( {k - {1/2\sqrt{\beta^{2} + Q^{2}}}} \right)}}{{{f\left( {Q,k,\beta} \right)}}^{2} + {2N\; k\text{/}{k_{z}\left( {Q\text{/}2} \right)}}}.}} & (40) \end{matrix}$

The object structure is then given by

$\begin{matrix} {{{\overset{\sim}{\overset{\sim}{\eta}}}^{+}\left( {Q,\beta} \right)} = \left\lbrack \frac{{f^{*}\left( {Q,k,\beta} \right)}{\overset{\sim}{S}\left( {Q,k} \right)}}{{{f\left( {Q,k,\beta} \right)}}^{2} + {2N\; k\text{/}{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}} & (41) \end{matrix}$

The object structure in the coordinate domain is obtained by applying the three-dimensional inverse Fourier transform.

To achieve phase stability of the signal, a microscope coverslip (not shown) may be placed on top of sample 8 and the top reflection from the air-coverslip interface acts as a fixed reference delay relative to the object. The delay fluctuations of the interferometer are removed from each cross-correlation interferogram by locating the air-coverslip reflection in each interferogram, estimating the phase and group delay of the reflection, and applying the opposite phase and group delay to the entire interferogram. Prior to processing, the spectra, each representing a column of depth-dependent data, are assembled adjacently as the beam is transversely scanned over the sample. The detected digital signal is interpolated to account for the non-uniform sampling of the spectrum and to compensate for up to third-order dispersion. Specifically, the signal is interpolated by a factor of two by a band-limiting interpolator implemented using the fast Fourier transform (FFT). This prepares the signal for the cubic B-spline interpolation, which has a transfer function with an amplitude that attenuates frequencies close to the Nyquist limit. The cubic B-spline interpolator resamples the spectrum to a uniform frequency space according to a calibration procedure utilizing a single reflector placed at the focus of the objective lens. Sample movement, inducing phase and group delay changes, is tracked using a reference microscope coverslip, and the deviations are corrected. At this point, the quantity S(r0, k), in Eq. (1) has been estimated. Next, the two-dimensional FFT in the transverse directions is calculated to yield {tilde over (S)}(Q,k). Then, the non-uniform ISAM resampling and filtering of Eq. (3) using cubic B-splines is implemented to yield {tilde over ({tilde over (η)}. Finally, the 3-D inverse FFT is used to attain the ISAM reconstruction, an estimate of η(r).

By application of ISAM techniques as described, in vivo imaging may advantageously be performed on larger volumes of tissue than volumes that would otherwise have to be resected. Furthermore, ISAM achieves high-speed, high-resolution imagery without need for the timely processing, sectioning, and staining of a resection.

With the use of near-infrared light, high-resolution ISAM facilitates the noninvasive monitoring of cellular and nuclear development with penetration depths up to 3 mm. Of course, in regions of extreme scattering or absorption penetration depths may be reduced.

Image formation algorithms are characterized differently than image post-processing routines. In particular, ISAM is a unique image formation method that utilizes the fundamental resolution capabilities of the acquired optical signal based on the physics of the scattering within the detection beam. In contrast, a simple image post-processing algorithm may attempt to extrapolate beyond the information inherent an image. For example, maximum likelihood, blind-deconvolution, or entropy-constrained algorithms can effectively produce energy compaction as an estimated solution to an image reconstruction. Such estimation may incorrectly reconstruct features in an image, thus misrepresenting the true biological structure and potentially leading to an incorrect diagnosis. ISAM is not based on estimation, thus such misrepresentations do not exist. Furthermore, estimation algorithms often exceed the limited computational complexity necessary for real-time imaging. The ISAM image formation algorithm can be implemented with computational complexity of O(N log N), where N is the number of volume elements to resolve, which makes ISAM amenable to real-time imaging. Furthermore, the ISAM algorithm can be applied to planes as well as volumes, thus enhancing cross-sectional imaging.

Azimuthally-Scanned Implementation

Embodiments of the invention are now described in which a focused beam is directed perpendicular to an OCT catheter, which might, for example, be incorporated into an endoscope. An endoscope, used for exploring the tubular lumens within the human gastrointestinal tract, typically consists of a long, flexible device of 1 cm diameter or less. Inside the endoscope, in addition to a source of white light illumination and optics for imaging, for example, on a charge-coupled device (CCD) detector, are working channels through which various instruments for biopsy or manipulating tissue are passed. For example, tissue biopsy samples can be extracted and withdrawn by forceps or suction. Smaller diameter catheters are used in the cardiovascular system, e.g. for the insertion of balloons for angioplasty or to deploy stents. Intravascular catheters minimize invasiveness and provide access to vascular lesions associated with cardiovascular disease.

An azimuthally-scanned OCT system would typically include a working channel containing a single-mode optical fiber, a focusing lens (typically a graded index lens cemented or fused to the fiber), and a right-angle prism or a custom cleaved surface for reflecting the beam by 90 degrees to the side of the catheter.

Fiber-optic OCT catheters have been integrated with endoscopes to image the esophagus, colon, and other internal organs and mucosal tissue, as described, for example, by Tearney et al., In vivo endoscopic optical biopsy with optical coherence tomography, Science, vol. 276, pp. 2037-39 (1997), incorporated herein by reference. In instruments based on fiber-optic OCT, the illumination originates inside the object or tubular lumen being imaged, and is usually scanned azimuthally around the long axis of the catheter. As the catheter is azimuthally scanned and translated along the long-axis of the catheter, a 3-D image of the object is acquired. Because the beam is typically focused at a fixed distance from the catheter, the depth-of-focus of the resulting images is confined to a narrow annulus.

By rotating the catheter about its long-axis, the beam may be directed along any path perpendicular to the axis. By pushing or pulling the catheter, the beam is translated along the long-axis of the catheter. Together these two degrees of freedom enable the instrument to scan a cylindrically shaped volume around the catheter. Typical imaging with this catheter design involves acquisition of axial scans (either in the time or frequency domain) while rotating the catheter through 360 degrees, advancing the catheter a small distance along its long-axis, and repeating the measurement. After acquisition, one possesses a data set parameterized by the illumination frequency (or time delay), the angular coordinate of the catheter during the scan, and the translational position of the catheter along its axis. With our solution of the inverse problem, we infer the object susceptibility from these data.

An algorithm that infers the susceptibility of a scatterer from the signal acquired in angularly scanned OCT is now described. These may be advantageously employed in catheter-based optical coherence tomography, but the scope of the present invention is not limited and may include application in endoscopic or intravascular ultrasound as well. Other applications may include acoustic, sonar, and seismic sensing where the imaged object is close to a focused transducer, and radar sensing of objects near a rotating dish antenna.

The Forward Problem for Azimuthally-Scanned ISAM

In contradistinction to the forgoing discussion wherein the illuminating Gaussian beam was translated in a straight line perpendicular to its axis, in the following discussion, rotation of the Gaussian beam is considered about the origin.

We consider an experiment in which a Gaussian beam originates at a position with Cartesian coordinates (0, p, 0). Let us denote Cartesian coordinates fixed relative to the sample by r=(x, y, z) and let us denote Cartesian coordinates fixed relative to the beam by r′=(x′, y′, z′). For each fixed axial position of the fiber y=y′=p. The beam is directed at an angle θ from the z-axis, and along the z′ axis. The coordinates may be related by a rotation matrix R(θ) so that r=R(θ)r′ where

$\begin{matrix} {{R(\theta)} = {\begin{pmatrix} {\cos \; \theta} & 0 & {\sin \; \theta} \\ 0 & 1 & 0 \\ {{- \sin}\; \theta} & 0 & {\cos \; \theta} \end{pmatrix}.}} & (42) \end{matrix}$

The beam is focused a distance z0 from the y axis. The field is polychromatic with power spectrum A2(k) where k=ω/c is the wave number associated with frequency ω. The width of the beam waist is a function of frequency given by W(k)=α/k, where α=π/NA, and NA, as above, is the numerical aperture of the focused beam. The beam is rotationally scanned so that the signal is sampled for all angles −π≦θ<π, and the beam is also translated along the y axis to cover all axial coordinates p. FIG. 21 illustrates this notation.

In the discussion above, it was assumed that the direction of propagation of the beam was fixed to be along the z direction. The location of the center of the beam in the waist plane was given by r0. Then the signal measured in the interferometer is given by the expression {tilde over (S)}(r,k) which is given by

$\begin{matrix} {{{\overset{\sim}{S}\left( {r,k} \right)} = {{\left( {2\pi} \right)}^{- 2}{A(k)}k^{- 1}{\int\limits_{V}{{^{3}r}\; {\eta (r)}{f^{2}\left( {{r - r_{0}};k} \right)}}}}},} & (43) \end{matrix}$

Where η(r) is the susceptibility of the sample being probed, f²(r′;k) is given by the expression:

$\begin{matrix} {{f^{2}\left( {r^{\prime};k} \right)} = {\frac{1}{\left( {2\; \pi} \right)^{2}}{\int{{^{2}{\xi exp}}\left( {{- }\; {\xi \cdot r^{\prime}}} \right)\frac{1}{2}\left( {\frac{\alpha^{2}}{k^{2}} + \frac{\left( {z^{\prime} - z_{0}} \right)}{k}} \right)^{- 1}{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4\; k^{2}}} \right)}{\exp \left\lbrack {{\left( {z^{\prime} - z_{0}} \right)}\sqrt{\left( {2\; k} \right)^{2} - \xi^{2}}} \right\rbrack}}}}} & (44) \end{matrix}$

where ξ=(ξ_(x), ξ_(y), 0) and the integral is over the plane. Note that we do not now make the paraxial approximation for the phase term. The signal depends on frequency, position along the y-axis, and the angle of propagation of the beam as described above. This signal, {tilde over (S)}(k, p, θ), may be found from Eq. (39) by writing the integrand in the coordinates stationary with respect to the beam. Thus we obtain

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {{\left( {2\pi} \right)}^{- 2}{A(k)}k^{- 1}{\int\limits_{V}{{^{3}r^{\prime}}{\eta \left\lbrack {{R(\theta)}r^{\prime}} \right\rbrack}{{f^{2}\left( {{r^{\prime} - {p\hat{y}}};k} \right)}.}}}}} & (45) \end{matrix}$

By substituting Eq. (44) into Eq. (45) and rearranging terms, we find

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{}{2}{A(k)}k^{- 1}{\int{{^{2}{{\xi exp}\left\lbrack {{- }\; z_{0}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}}{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}{\quad{\int{{^{3}r^{\prime}}{\exp \left\lbrack {{- }\; {\xi \cdot \left( {r^{\prime} - {p\hat{y}}} \right)}} \right\rbrack}{{\eta \left\lbrack {{R(\theta)}r^{\prime}} \right\rbrack}\left\lbrack {\frac{\alpha^{2}}{k^{2}} + \frac{\left( {z^{\prime} - z_{0}} \right)}{k}} \right\rbrack}^{- 1}{{\exp \left\lbrack {\; z^{\prime}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}.}}}}}}}} & (46) \end{matrix}$

In our analysis of the OCT inverse problem on a Cartesian grid, we found that under certain reasonable approximations, the data could be related to the object susceptibility through a resampling scheme in the Fourier domain. We derive a similar relation here. To do so, it will be advantageous to replace

$\left\lbrack {\frac{\alpha^{2}}{k^{2}} + \frac{\left( {z^{\prime} - z_{0}} \right)}{k}} \right\rbrack$

with an approximation commensurate with the natural geometry of the problem. Explicitly, we replace z′ with ρ′=√{square root over (z′²+x′²)}. For most OCT systems, the bandwidth is a small fraction of the central frequency and so we replace

$\frac{1}{k^{2}}$

with

$\frac{1}{k\; k_{0}}.$

Thus the factor

$\left\lbrack {\frac{\alpha^{2}}{k^{2}} + \frac{\left( {z^{\prime} - z_{0}} \right)}{k}} \right\rbrack$

is replaced by

${\frac{1}{k}\left\lbrack {\frac{\alpha^{2}}{k_{0}} + {\left( {\sqrt{x^{\prime 2} + z^{\prime 2}} - z_{0}} \right)}} \right\rbrack}.$

This expression is slowly varying relative to the rapidly varying phase of the term exp └iz′√{square root over ((2k)²−ξ²)}┘, and so approximations to it tend not to change the result greatly. With this substitution,

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{}{2}{A(k)}{\int{{^{2}{{\xi exp}\left\lbrack {{- }\; z_{0}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}}{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}{\int{{^{3}r^{\prime}}{\exp \left\lbrack {{- }\; {\xi \cdot \left( {r^{\prime} - {p\hat{y}}} \right)}} \right\rbrack}{{\eta \left\lbrack {{R(\theta)}r^{\prime}} \right\rbrack}\left\lbrack {\frac{\alpha^{2}}{k_{0}} + {\left( {\rho^{\prime} - z_{0}} \right)}} \right\rbrack}^{- 1}{{\exp \left\lbrack {\; z^{\prime}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}.}}}}}}} & (47) \end{matrix}$

To evaluate this integral, we change variables in the inner integral to the coordinates stationary in the reference frame of the sample,

$\begin{matrix} {{{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{}{2}{A(k)}{\int{{^{2}{{\xi exp}\left\lbrack {{- }\; z_{0}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}}{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}{\exp \left( {\; \xi_{y}p} \right)}{\int{{^{3}r}\; \exp \left\{ {{- {\left\lbrack {\xi - {\hat{z}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}}} \right\rbrack}} \cdot {R\left\lbrack {\left( {- \theta} \right)r} \right\rbrack}} \right\} \; {{\eta (r)}\left\lbrack {\frac{\alpha^{2}}{k_{0}} + {\left( {\rho - z_{0}} \right)}} \right\rbrack}^{- 1}}}}}}},} & (48) \end{matrix}$

where ρ=ρ′=√{square root over (x²+z²)}. It may be seen that the integral over r results in a Fourier transform if we note that └ξ−{circumflex over (z)}√{square root over ((2k)²−ξ²)}┘·R(−θ)r=R(θ)└ξ−{circumflex over (z)}√{square root over ((2k)²−ξ²)}┘·r, after which we obtain

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{}{2}{A(k)}{\int{{^{2}{{\xi exp}\left\lbrack {{- }\; z_{0}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}}{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}{\exp \left( {\; \xi_{y}p} \right)}\overset{\sim}{\eta}\left\{ {- {{R(\theta)}\left\lbrack {\xi - {\hat{z}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}}} \right\rbrack}} \right\}}}}} & (49) \end{matrix}$

where {tilde over ({tilde over (η)}(β) is the weighted Fourier transform of η(r) given by

$\begin{matrix} {{\overset{\sim}{\eta}(\beta)} = {\int^{\;}{{^{3}r}\mspace{11mu} {\exp \left( {\; {r \cdot \beta}} \right)}{{{\eta (r)}\left\lbrack {\frac{\alpha^{2}}{k_{0}} + {\left( {\rho - z_{0}} \right)}} \right\rbrack}^{- 1}.}}}} & (50) \end{matrix}$

To change the integral over to a cyclic convolution, we make the substitution √{square root over ((2k)²−ξ_(y) ²)}cos φ=ξ_(x) so that √{square root over ((2k)²−ξ_(y) ²)} sin φ=√{square root over ((2k)²−ξ²)}, after which we obtain

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{}{2}{A(k)}{\int{{\xi_{y}}\mspace{11mu} {\exp \left( {{\xi}_{y}p} \right)}{\int_{0}^{\pi}\ {{\varphi}\left\{ {\left\lbrack {\sqrt{\left( {2k} \right)^{2} - \xi_{y}^{2}}\sin \mspace{11mu} \varphi} \right\rbrack {\exp \left\lbrack {{- }\; z_{0} \sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack} {\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}} \right\} \overset{\sim}{\eta}{\left\{ {- {{R(\theta)}\left\lbrack {{\hat{x}\mspace{14mu} \cos \mspace{11mu} \varphi \sqrt{\left( {2k} \right)^{2} - \xi_{y}^{2}}} + {\hat{y\;}\xi_{y}} - {\hat{z}\mspace{14mu} \sin \mspace{11mu} \varphi \sqrt{\left( {2k} \right)^{2} - \xi_{y}^{2}}}} \right\rbrack}} \right\}.}}}}}}} & (51) \end{matrix}$

For brevity, we define the kernel function K(k, ξ_(y), φ).

$\begin{matrix} {{K\left( {k,\xi_{y},\varphi} \right)} = {\frac{}{2}{{A(k)}\left\lbrack {\sqrt{\left( {2k} \right)^{2} - \xi_{y}^{2}}\sin \mspace{11mu} \varphi} \right\rbrack}{\exp \left\lbrack {{- }\; z_{0}\sqrt{\left( {2k} \right)^{2} - \xi^{2}}} \right\rbrack}{{\exp \left( {- \frac{\xi^{2}\alpha^{2}}{4k^{2}}} \right)}.}}} & (52) \end{matrix}$

We note that the cos φ next to x and the sin φ next to {circumflex over (z)} in Eq. (51) effect a rotation in the x-z plane through an angle −φ of a vector x√{square root over ((2k)²−ξ_(y) ²)}. Given this, we can express Eq. (51) as a cyclic convolution:

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\int{{\xi_{y}}\mspace{11mu} {\exp \left( {\; \xi_{y}p} \right)}{\int_{0}^{\pi}\ {{\varphi}\mspace{11mu} {K\left( {k,\xi_{y},\varphi} \right)}\overset{\sim}{\eta}{\left\{ {{- R}{\left( {\theta - \varphi} \right)\left\lbrack {{\hat{x}\; \sqrt{{\left( {2k} \right)^{2} - \xi_{y}^{2}}\;}} + {\hat{y\;}\xi_{y}}} \right\rbrack}} \right\}.}}}}}} & (53) \end{matrix}$

By combining the rotations R(θ) and R(−φ), we find the integral over φ is a cyclic convolution. This cyclic convolution can be performed efficiently using the product of Fourier series. To put Eq. (51) into diagonal form, we define the following functions of the data, the kernel, and the structure function:

$\begin{matrix} {\mspace{85mu} {{{\overset{\approx}{S}\left( {k,\xi_{p},n_{\theta}} \right)} = {\underset{- \infty}{\int\limits^{\infty}}{\int\limits_{- \pi}^{\pi}{{p}{\; \theta}\mspace{11mu} {\exp \left( {\; p\; \xi_{p}} \right)}{\exp \left( {{\theta}\; n_{\theta}} \right)}{\overset{\sim}{S}\left( {k,p,\theta} \right)}}}}},}} & (54) \\ {\mspace{79mu} {{{\overset{\sim}{K}\left( {k,\xi_{y},n_{\theta}} \right)} = {\int\limits_{0}^{\pi}{{\theta}\mspace{11mu} {\exp \left( {{\theta}\; n_{\theta}} \right)}{K\left( {k,\xi_{y},\theta} \right)}}}},}} & (55) \\ {{\overset{\approx}{\eta}\left( {k,\xi_{y},n_{\theta}} \right)} = {\int\limits_{- \pi}^{\pi}{{\theta}\mspace{11mu} {\exp \left( {{\theta}\; n_{\theta}} \right)}\overset{\sim}{\eta}{\left\{ {- \left\lbrack {{\hat{x}\mspace{11mu} \cos \; \theta \sqrt{{\left( {2k} \right)^{2} - \xi_{y}^{2}}\;}} + {\hat{y\;}\xi_{y}} + {\hat{z}\mspace{11mu} \sin \mspace{11mu} \theta \sqrt{{\left( {2k} \right)^{2} - \xi_{y}^{2}}\;}}} \right\rbrack} \right\}.}}}} & (56) \end{matrix}$

Where n_(θ) is an integer on [−∞,∞]. If we insert the definitions of Eqs. (36)-(38) into Eq. (35), we find the following relationship:

{tilde over ({tilde over (S)}(k,ξ _(p) ,n _(θ))={tilde over (K)}(k,ξ _(p) ,n _(θ)){tilde over ({tilde over (η)}(k,ξ _(p) ,n _(θ)).  (57)

In this form we see that {tilde over ({tilde over (S)} and {tilde over ({tilde over (η)} are related by a diagonal integral operator whose kernel is {tilde over (K)}(k′, ξ_(p′), n_(θ′))δ(k−k′)δ(ξ_(p)−ξ_(p′))δ_(n) ₀ ,n_(θ′). Explicitly S=K{tilde over ({tilde over (η)} where {circumflex over (K)} is the integral operator

$\begin{matrix} {{\left\lfloor {K\; \overset{\approx}{\eta}} \right\rfloor \left( {k,\xi_{p},n_{0}} \right)} = {\int{{k^{\prime}}{\int{{\xi_{p^{\prime}}}{\sum\limits_{n_{\theta}}^{\;}\; {{\overset{\sim}{K}\left( {k^{\prime},\xi_{p^{\prime}},n_{\theta^{\prime}}} \right)}{\delta \left( {k - k^{\prime}} \right)}{\delta \left( {\xi_{p} - \xi_{p^{\prime}}} \right)}\delta_{n_{\theta},n_{\theta^{\prime}}}{{\overset{\approx}{\eta}\left( {k^{\prime},\xi_{p^{\prime}},n_{\theta^{\prime}}} \right)}.}}}}}}}} & (58) \end{matrix}$

This diagonal operator will simplify finding solutions to specific inverse problems.

The Inverse Problem for Azimuthally-Scanned ISAM

Eq. (57) defines a linear relationship between the object structure and data. To better understand how to invert this relationship, the relationship between the data {tilde over (S)}(k, p, θ) and the object η(r) is written explicitly:

$\begin{matrix} {{\overset{\sim}{S}\left( {k,p,\theta} \right)} = {\frac{1}{4\pi^{2}}{\int{{\xi_{y}}\mspace{11mu} {\exp \left( {{- {\xi}_{y}}p} \right)}{\sum\limits_{n_{\theta} = {- \infty}}^{\infty}\; {{\exp \left( {{- }\; \theta \; n_{\theta}} \right)}{K\left( {k,\xi_{y},n_{\theta}} \right)}{\int{{^{3}r}\; {{\eta (r)}\left\lbrack {\frac{\alpha^{2}}{k_{0}} + {\left( {\rho - z_{0}} \right)}} \right\rbrack}^{- 1}{\underset{- \pi}{\int\limits^{\pi}}{{\varphi}\mspace{11mu} {\exp \left( {\; \theta \; n_{\theta}} \right)}\exp \left\{ {{- }\; {r \cdot {{R(\varphi)}\left\lbrack {{\hat{x}\sqrt{\left( {2k} \right)^{2} - \xi_{y}^{2}}} + {\hat{y}\; \xi_{y}}} \right\rbrack}}} \right\}}}}}}}}}}} & (59) \end{matrix}$

Where {tilde over (K)}(k, ξ_(p), n_(θ)) is given explicitly by

$\begin{matrix} {{\overset{\sim}{K}\left( {k,\xi_{p},n_{\theta}} \right)} = {\frac{}{2}{A(k)}{\int\limits_{0}^{\pi}{{\theta}\mspace{11mu} {\exp \left( {\; \theta \; n_{\theta}} \right)}{\exp \left\lbrack {{- \frac{{\left( {2k} \right)^{2}\cos^{2}\theta} + {\xi_{p}^{2}\mspace{11mu} \sin^{2}\theta}}{2}}\frac{\alpha^{2}}{2k^{2}}} \right\rbrack}{\exp \left\lbrack {{- }\; z_{0}\sin \mspace{11mu} \theta \sqrt{\left( {2k} \right)^{2} - \xi_{p}^{2}}} \right\rbrack}\sqrt{\left( {2k} \right)^{2} - \xi_{p}^{2}}\sin \mspace{11mu} {\theta.}}}}} & (60) \end{matrix}$

Eq. (59) can be rewritten to use a Fredholm-type kernel κ(k, p, θ, r) such that

S(k,p,θ)=κη=∫d ³ rκ(k,p,θ,r)η(r).  (61)

Although Eq. (61) may not be strictly solvable, a least-squares solution η⁺ can be found by minimizing a functional:

$\begin{matrix} {{{\eta^{+} = {{\underset{\eta}{{argmin}}S} - {\kappa\eta}}}}^{2} = {\underset{\eta}{argmin}{\int\limits_{0}^{\infty}{{k}{\overset{\infty}{\int\limits_{- \infty}}{{p}{\overset{\pi}{\int\limits_{- \pi}}{{\theta}{{{{S\left( {k,p,\theta} \right)} - {{\kappa\eta}(r)}}}^{2}.}}}}}}}}} & (62) \end{matrix}$

The least-squares solution is then given by the pseudo-inverse η⁺=(κ^(†)κ)⁻¹κ^(†)S. While this solution is formally correct, the inverse (κ^(†)κ)⁻¹ can be difficult to compute in practice. Instead, we find the least-squared error solution for the weighted Fourier transform {tilde over ({tilde over (η)}⁺ that, while not directly minimizing the error relative to the measurements, still constrains the estimated object structure to be consistent with the data:

$\begin{matrix} {{\overset{\approx}{\eta}}^{+} = {{{\underset{\overset{\approx}{\eta}}{argmin}{{S - {K\; \overset{\approx}{\eta}}}}^{2}} + {\lambda {\overset{\approx}{\eta}}^{2}}} = {{\underset{\overset{\approx}{\eta}}{argmin}{\int\limits_{0}^{\infty}{{k}{\overset{\infty}{\int\limits_{- \infty}}{{\xi_{p}}{\sum\limits_{n_{\theta} = {- \infty}}^{\infty}\; {{{\overset{\approx}{S}\left( {k,\xi_{p},n_{\theta}} \right)} - {{K\left( {k,\xi_{p},n_{\theta}} \right)}{\overset{\approx}{\eta}\left( {k,\xi_{p},n_{\theta}} \right)}}}}^{2}}}}}}} + {\lambda {{{\overset{\approx}{\eta}\left( {k,\xi_{p},n_{\theta}} \right)}}^{2}.}}}}} & (63) \end{matrix}$

This least-squares solution keeps the object estimate consistent with Eq. (57). Also included is a Tikhonov regularization term to stabilize the solution, with regularization parameter λ. The solution {tilde over ({tilde over (η)}⁺ is:

$\begin{matrix} {{{\overset{\approx}{\eta}}^{+}\left( {k,\xi_{p},n_{\theta}} \right)} = {\frac{{\overset{\approx}{S}\left( {k,\xi_{p},n_{\theta}} \right)}{K^{*}\left( {k,\xi_{p},n_{\theta}} \right)}}{{{K\left( {k,\xi_{p},n_{\theta}} \right)}}^{2} + \lambda}.}} & (64) \end{matrix}$

This least squares solution is a numerically simpler method of estimating the object structure. Starting with data given by S(k, p, θ) we can compute {tilde over ({tilde over (S)}(k, ξ_(p), n_(θ)) using Eq. (52). Using Eq. (64) one can compute {tilde over ({tilde over (η)}⁺(k, ξ_(p), n_(θ)). Then Eq. (56) can be solved for {tilde over (η)}⁺ by taking the discrete inverse Fourier transform of {tilde over ({tilde over (η)}⁺ with respect to n_(θ). Finally, a 3-D inverse Fourier transform computes η⁺(r) from {tilde over (η)}⁺. In the limit that λ→0 and all data are continuously available, this approach yields an exact solution for η(r). In the more realistic scenario that a regularized solution is employed, a stable solution is obtained.

Simulation of Azimuthally-Scanned ISAM

As in the full-field OCT embodiment discussed above, the azimuthally-scanned algorithmic embodiment is now demonstrated by implementing a simulation of the forward and inverse scattering in the radial OCT geometry. A synthetic object was created comprised of pointlike scatterers. The simulated OCT data were calculated from the exact forward problem using Eq. (45), and then the regularized solution of the inverse scattering solution was calculated using Eq. (64). The simulation is of a pseudo-three-dimensional object that is invariant along the y-axis, so that the object is effectively two-dimensional.

The simulation was performed with lengths in units of the central wavelength of the illumination. Typical center wavelengths for OCT imaging are between 800 nm and 1400 nm. The cross-section of the simulated object was taken to be approximately 135 by 135 wavelengths. The Gaussian illumination beam was assumed to be focused 45 wavelengths from the origin, with a beam waist width of 2.5 wavelengths. The scatterers were placed 15 to 60 wavelengths from the origin at randomly selected angles relative to the x-axis. The simulated source was taken to have a Gaussian spectrum with a full-width-half-maximum (FWHM) fractional bandwidth of approximately 25%. Each of the scatterers had the same susceptibility.

The forward scattering problem was implemented by directly summing the contribution of each point scatterer individually using Eq. (45). This was achieved by summing for each sampled data point {tilde over (S)}(k,θ) the total collected backscattered amplitude for all of the scatterers at their respective positions r′ the amplitude f²(r′;k) as specified in Eq. (44). Note that in Eq. (44) the exact phase rather than the Fresnel quadratic approximation was used to more accurately compute the data for a high numerical aperture beam. To show the equivalent OCT image, the data was inverse Fourier transformed along the k axis, yielding S(r,θ). The resulting S(r,θ) is displayed in a polar plot in FIG. 23( a).

The dotted circle in the diagram indicates the radius at which the Gaussian beam is focused. Note that the images of points located closer to the origin than the focus (inside the circle) curve towards the origin, and the points located further from the origin than the focus curve (outside the circle) away from the origin, as would be expected.

The inverse scattering problem was implemented using the approximate solution embodied in Eq. (64). The data is given as {tilde over (S)}(k,θ). To utilize Eq. (64), several Fourier transform steps were needed. The inverse scattering algorithm was implemented using the following steps:

-   -   The data {tilde over (S)}(k,θ) was Fourier transformed with         respect to θ to yield {tilde over ({tilde over (S)}(k,n_(θ)).     -   The function {tilde over (K)}(k,θ) was calculated (using         ξ_(p)=0) and then Fourier transformed with respect to θ to yield         {tilde over (K)}(k,n_(θ)) as per Eq. (61).     -   The regularized {tilde over ({tilde over (η)}⁺(k,n_(θ)) was         calculated using Eq. 65.     -   {tilde over ({tilde over (η)}⁺(k,n_(θ)) was inverse Fourier         transformed with respect to n_(θ) yield {tilde over (η)}⁺(k,θ).     -   The {tilde over (η)}⁺(k,θ) was inverse Fourier transformed with         respect to k to yield η_(R) ⁺(l,θ), the Radon transform of         η⁺(x,z).     -   The inverse Radon transform of η_(R) ⁺(l,θ) was performed to         yield η⁺(x,z), the Tikhonov-regularized inverse.

The inverse Radon transform was used as a convenient way to convert from the polar representation of the Fourier transform {tilde over (η)}⁺(k,θ) to its inverse Fourier transform Cartesian counterpart η⁺(x,z), using the Fourier projection slice theorem. Unfortunately, many implementations of the inverse Radon transform, such as the filtered-backprojection method that was used for this simulation, are slow, and therefore care will need to be exercised to ensure that the computational burden is not too great. Methods exist to implement the inverse

Radon transform in O(N² log N) time, rather than the O(N³) typical of most filtered-backprojection inverse Radon transform methods.

The results of the inverse scattering computation are shown in FIG. 23( b). As can be seen, the blurred arcs corresponding to the point sources in the uncorrected OCT data are corrected to be pointlike when inverse scattering is performed on the data. The algorithm correctly compensates for the range-dependent blur and curvature of the backscattered signal. Unlike in the translationally-scanned Gaussian beam or the full-field cases, the reconstructed image does not exhibit uniform resolution. The resolution of the reconstruction depends on the distance from the origin. Because the beam width is wide near the origin, points nearer the origin than the focus are overlapped by the beam for many angles □, so that the resolution of points near the origin is high. At the focus, the beam width is narrow and so points near the focus are also resolved well. Far from the origin, the beam is wide and points are only overlapped by the beam for a narrow range of angles given by the divergence of the beam, so that the resolution degrades with distance from the origin. Generally, the resolution is nearly constant between the origin and the focus radius, and slowly degrades to a constant angular resolution at radii further than the focus. Therefore, the most useful resolution will be achieved for distances at or closer than the focus radius.

To explore the range-dependent resolution further, a simulation of point scatterers reconstructed with beams with various widths and focus radii is now described with reference to FIG. 24. FIG. 24 has four parts, each of which is the simulated resolution of point scatterers for beams of different widths. The marking next to each curve is the focus radius for each simulated beam. The resolution is measured as the FWHM of the reconstructed point in the angular direction. Each graph relates the FWHM resolution to the distance from the axis to the simulated point. For small beam waists, as in parts (a), (b), and (c), the resolution is approximately constant for radii closer than the focus radius. Further than the focus the FWHM resolution starts to increase. For the wider beams, the transverse resolution near the origin can be somewhat better than the width of the beam waist.

To examine the validity of the approximation made in Eq. 47 of small fractional bandwidth, we simulate the reconstruction of point scatterers imaged with various source bandwidths. The simulated focus radius is 25 wavelengths, and the beam widths are 1.5 and 5 wavelengths. FIG. 25 shows the FWHM axial resolution as a function of fractional bandwidth. The resolution should be approximately half the reciprocal of the fractional bandwidth, to which the simulation conforms.

Phase Stability in ISAM

The increased resolution gained by the ISAM solution relies upon phase stable measurements. The phases in cross-correlation signals correspond to the measured relative delay between the reference and sample signal at particular temporal frequencies of the illumination. The aforementioned methods rely on the phases of the cross-correlation measurements for a particular data set to correspond, i.e. the relative delays measured for various positions of the illumination beam need to reflect the true delays for the beam to scatter off of layers inside the object. Unfortunately, because of motions and changes in the object during the data acquisition, and thermal fluctuations that cause object dimensions to change, these delays can vary during the data acquisition interval. This is a problem for almost all computed imaging modalities, but can be exacerbated for optical imaging because the small size of the illumination wavelength (often less than a micron) means that very small motions can cause relatively large fluctuations in phase. If the data acquisition is brief, and the reference delay mechanism can produce a reliably repeatable delay to an accuracy of less than a wavelength, then phase stability between measurements can be easily achieved. For example, with the use of spectral detection for OCT, spectral-domain OCT (SD-OCT) seen in FIG. 20, we can be assured of phase stability within each axial data set because the reference mirror is typically fixed and the data acquisition is very rapid, typically occurring in fractions of a second. Specifically, each axial acquisition is determined directly from Fourier transform of the ensemble of spectral intensity measurements over the duration of the exposure time on a CCD camera. Thus, relative phases between adjacent reflections in the sample are fixed relative to each other and the reference for a single axial acquisition. Furthermore, if adjacent axial scans may be captured fast enough to avoid some minimum amount of phase drift then an accurate reconstruction is possible. Phase drift can occur in a system for multiple reasons including thermal changes, galvanometer or stage positioning accuracy, and system or sample jitter. The greater the time interval between scans, the more likely it is that random phase errors will occur. Adjacent axial scans in a single cross-sectional scan are thus less likely to suffer from distortions due to random phase jitter than adjacent axial scans from multiple cross-sectional scans.

Object reconstruction requires the phase to be stable relative to all axial scans of a 3D acquisition. There are several ways to achieve phase stability, whether it is one of many hardware and environmental configurations, implementations of reference objects, or algorithmic developments based on priors. In conventional scanned beam OCT, it has been shown by Ralston et al., Phase Stability Technique for Inverse Scattering in Optical Coherence Tomography, IEEE International Symposium on Biomedical Imaging., pp. 578-581, (2006), incorporated herein by reference, that one such possible method to achieve 3D phase stability in OCT for reconstruction of the inverse scattering solution is to use a flat reference reflector such as a microscope coverslip. Because the coverslip typically remains in contact with the object, its position relative to the object is fixed, and therefore can serve to indicate a delay that is consistent between axial scans. Such a method offers advantages over expensive environmental controllers and extremely fast acquisition hardware. Further, we develop an algorithm for tracking the air-glass interface. Other interfaces that are fixed relative to the object being measured can also be used, such as the interior or exterior surface of the transparent wall of a catheter.

The acquired SD-OCT signal can be represented after dispersion correction as a function of transverse position and wave number, S(r0,k), where the wave numbers k are related to the frequencies ω by the dispersion relation k(ω)=ω n/c, and n is the index of refraction.

We present a method that analyzes each axial scan individually and applies a phase to compensate variations of the position of the sample relative to the illumination beam. We place a reflective surface such as a microscope coverslip on top of the sample to act as a reference surface, which is used to infer the delay to the top surface of the sample. The signal for an arbitrary axial line of data can be represented as S(k), a function of k. We assume that there is a range of distances along the illumination beam zmin to zmax for which the signal reflected from the coverslip is known to reside in every axial scan. The inverse Fourier transform of S(k) is computed as Sc(z), and the signal corresponding to the reflection is contained in the samples Sc(z) for zmin<z<zmax. The spatial spectrum of the reflection is computed as the Fourier transform of Sc(z) over the window zmin<z<zmax, which is called {tilde over (S)}_(c)(k).

Because the signal contained in {tilde over (S)}_(c)(k) corresponds to a single reflection, it is reasonable to model it as {tilde over (S)}_(c)(k)=A(k)e^(iφ(k)), where the phase function φ(k)=φ0+kd, where φ0 is an arbitrary phase and d is the true position of the surface where the reference reflection occurs. Because of the motion of the sample, the actual phase arg {tilde over (S)}_(c)(k)=φ′(k). By multiplying the axial scan data S(k) by the correction factor e^(i[φ(k)−φ′(k)]), the phase of the axial scan can be adjusted to place the reflection at its true known position d.

We model the phase φ′(k), as a Taylor series around a center frequency k₀:

${{\varphi^{\prime}(k)} = {{{\varphi^{\prime}\left( k_{0} \right)} + {\left( {k - k_{0}} \right)\frac{\partial\varphi^{\prime}}{\partial k}}}_{k = k_{0}}{+ \ldots}}}\mspace{14mu},$

To utilize this model, we must estimate the value of ∂φ′/∂k|_(k=) ₀ from the data function φ′(k). The function φ′(k) is wrapped to the range −□ to □, so calculating the derivative directly from the wrapped data will incorrectly incorporate the 2□ jumps into the estimate. Instead, we form the unwrapped φ_(w)(k) by removing 2□ discontinuities from φ′(k). The estimate then becomes

$\frac{\partial\varphi^{\prime}}{\partial k}_{k = k_{0}}{\approx \frac{{\varphi_{w}\left( k_{2} \right)} - {\varphi_{w}\left( k_{1} \right)}}{k_{2} - k_{1}}}$

-   -   where k1<k0<k2, with the frequencies k1 and k2 chosen to span         the illumination spectrum, typically with k1 and k2         corresponding to the frequencies at which the power spectral         density is half of that at the peak.

Once φ′(k₀) and ∂φ′/∂k|_(k=k) ₀ are known, the empirical φ′(k) can be computed, and the corrected axial scan spectrum S′(k)=S(k)e^(i[φ(k)−φ(k′)]). This corrected axial scan data will be modified such that the position of the reference reflection is always at the same location on the axial scan, removing the effective longitudinal relative motion between the sample and the scanned beam. For this method to work properly, the reference object must be located for each axial scan, otherwise that axial scan could contribute to a poor reconstruction. Furthermore, refinements to this method could utilize higher order terms of the series for φ′(k), which would account for instrument dispersion as well as motion.

Experimental Examples of ISAM Imaging

A tissue phantom consisting of a collection of titanium dioxide scatterers having a mean diameter of 1 μm and uniformly suspended in silicone was imaged using low-coherence interferometry and a 0.05 NA objective. FIG. 26 displays cross-sections through an unprocessed data set (left) and ISAM reconstruction (right) of a volume 360 μm×360 μm (transverse)×2000 μm (axial). FIG. 26 a-f contain three pairs of en face sections for both the unprocessed data (FIG. 26 a-c) and the ISAM reconstructions (FIG. 26 d-f). The distances from the en face section planes to the focus, located at z=0, are z=1100 μm (FIGS. 26 a and 26 d), z=475 μm (FIGS. 26 b and 26 e), and z=−240 μm (FIGS. 26 c and 26 f). These sections show that the reconstruction has resolved the scatterers throughout a range of depths over nine times the Rayleigh range from the focus, where the Rayleigh range is commonly defined as half of the depth-of-field, or what is considered in-focus in optical imaging systems. In the unprocessed data, the interference between the signals scattered from adjacent scatterers is evident. Our method properly accounts for the diffraction of the beam, and so separates the superimposed signals from the scatterers to form well-resolved point images on all planes.

Human tumor tissue was resected and imaged ex vivo. Sections were marked with India ink after imaging and before embedding to register locations. FIG. 27 includes en face planes (Slices A and B) of the unprocessed data (FIG. 27 a) where the beam diffraction effects are evident, the computed ISAM reconstructions (FIG. 27 b), and images of corresponding registered histological sections (FIG. 27 c). Although embedding, sectioning, and staining of tissue can disrupt features to some degree, the registered histological sections provide prominent features for comparison. In the reconstruction, boundaries between adipose cells and the margin between adipose and fibrous tissue are clearly identified, with a strong correspondence to histology. While the histological images were obtained by destroying the sample, ISAM could readily be applied for in vivo applications because signal collection is in the backscattered epi-direction.

Real-Time Cross-Sectional Processing

In order to provide the benefits of spatially-invariant resolution attainable by means of the hitherto described features of ISAM and to obtain immediate feedback in time-critical situations or for monitoring transient dynamics, methods are now described for real-time realization of ISAM computations.

As described in detail above, an object being imaged by spectral-domain OCT (SD-OCT) has a susceptibility represented by η(r_(∥),z), where r∥ is the transverse position and z is the longitudinal position. The collected SD-OCT signal is represented by {tilde over (S)}(r_(∥),ω), whose arguments are the transverse position of the beam r∥ and the frequency ω. After correcting for dispersion, the signal is represented by {tilde over (S)}(r_(∥),k), where k is the uniformly spaced wavenumber. The Fourier transform of {tilde over (S)}(r_(∥),k) with respect to k is S(r_(∥),t). Introducing a coordinate change from t to t′ such that t′=0 coincides with the delay of the focal plane results in a signal S(r_(∥),t′). The 3-D Fourier transform of S(r_(∥),t′) is {tilde over ({tilde over (S)}(Q,k).

The algorithm for ISAM is constructed as described above. A solution for high-numerical aperture optics is implemented, namely, a relation is derived that associates the Fourier transform of the object η with the Fourier transform of the signal S. The 2-D Fourier transform of the spectral-domain OCT signal {tilde over (S)}(r_(∥),k) is given by the expression

$\begin{matrix} {{{\overset{\approx}{S}\left( {Q,k} \right)} = {\frac{k^{2}}{\alpha^{2}}{2\pi}^{2}{A(k)}\frac{^{{- 2}\; {k_{z}{({Q\text{/}2})}}z_{0}}}{k_{z}\left( {Q\text{/}2} \right)}^{\frac{{- \alpha^{2}}Q^{2}}{4k^{2}}}{\overset{\approx}{\eta}\left\lbrack {Q,{{- 2}{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack}}},} & (65) \end{matrix}$

where {tilde over ({tilde over (η)} is the 3-D Fourier transform of η, the argument Q is the transverse wavevector, k is the wavenumber, k₂(q)=√{square root over (k²−q²)}, z₀ is the fixed position of the beam focus, A(k) is the square root of the power spectral density, α=π/NA, and NA is the numerical aperture of the beam. The corresponding Tikhonov regularized solution, {tilde over ({tilde over (η)}⁺, takes the form

$\begin{matrix} {{{\overset{\approx}{\eta}}^{+}\left( {Q,\beta} \right)} = \left\lbrack \frac{{f^{*}\left( {Q,k,\beta} \right)}{\overset{\approx}{S}\left( {Q,k,} \right)}}{{{f\left( {Q,k,\beta} \right)}}^{2} + {2\lambda \; k\text{/}{k_{z}\left( {Q\text{/}2} \right)}}} \right\rbrack_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}} & (66) \\ {where} & \; \\ {{{f\left( {Q,k,\beta} \right)} = {\frac{k^{2}}{\alpha^{2}}{2\pi}^{2}{A(k)}\frac{^{{- 2}\; {k_{z}{({Q\text{/}2})}}z_{0}}}{k_{z}\left( {Q\text{/}2} \right)}^{\frac{{- \alpha^{2}}Q^{2}}{4k^{2}}}}},} & (67) \end{matrix}$

β is the longitudinal frequency coordinates of the object, and λ is the regularization constant. Rearranging the terms of the Fourier space into multiplicative factors of magnitude, {tilde over ({tilde over (B)}(Q,k), and phase, e^(i(2k) ^(z) ^((Q/2)z) ⁰ ^(+π/2)), the pseudo inverse can be rewritten as

$\begin{matrix} {{{{\overset{\sim}{\overset{\sim}{\eta}}}^{+}\left( {Q,\beta} \right)} = {{{\overset{\sim}{\overset{\sim}{B}}\left( {Q,k} \right)}^{{({{2{k_{z}{({Q/2})}}z_{0}} + {\pi/2}})}}{\overset{\sim}{\overset{\sim}{S}}\left( {Q,k} \right)}}_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}}},} & (68) \\ {where} & \; \\ {{\overset{\sim}{\overset{\sim}{B}}\left( {Q,k} \right)} = {\frac{{- \frac{k}{\alpha^{2}}}\pi^{2}{A(k)}^{\frac{{- \alpha^{2}}Q^{2}}{4k^{2}}}}{{\frac{k^{3}}{\alpha^{4}}\frac{2\pi^{4}{A^{2}(k)}}{k_{z}\left( {Q\text{/}2} \right)}^{\frac{{- \alpha^{2}}Q^{2}}{2k^{2}}}} + \lambda}.}} & (69) \end{matrix}$

Without loss of generality, the same origin is designated for the depth coordinates z as the time delay coordinates t. The t=0 delay corresponds to the z=0 plane and coincide at the path length matched delay of the reference. Additionally, for a coordinate change, the t′=0 delay corresponds to the z′=0 plane and coincide at the focal plane, where then z₀ will equal zero, and equation (66) reduces to

$\begin{matrix} {{{\overset{\sim}{\overset{\sim}{\eta}}}^{+ \prime}\left( {Q,\beta} \right)} = {{{\overset{\sim}{\overset{\sim}{B}}\left( {Q,k} \right)}^{{\pi}/2}{\overset{\sim}{\overset{\sim}{S}}\left( {Q,k} \right)}}_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}.}} & (70) \end{matrix}$

A coordinate change from t to t′ is achieved by circularly shifting the data. The origin of the t coordinates is at the time corresponding to the arrival of the reference light. The origin of the t′ coordinates is shifted such that t′=0 is at the focal plane. A zero pad of 2|t0| rows prevents aliasing of the shifted data, where t0 is the number of delay samples from the focus to t′=0. The model in FIG. 29( a) and the grid in FIGS. 29( b) and (c) describe visually in 2D the ISAM resampling seen in equation (70).

A shift of t0 in S(r_(∥),t) is used to make the t=0 delay coincide with the z=0 plane as will be seen in the algorithm. S(r_(∥),t+t₀) has the Fourier transform relation {tilde over ({tilde over (S)}(Q,k)e^(−ikt) ⁰ . If we substitute this into the equation.

$\begin{matrix} {{{\overset{\sim}{\overset{\sim}{\eta}}}^{+}\left( {Q,\beta} \right)} = {{{\overset{\sim}{\overset{\sim}{B}}\left( {Q,k} \right)}i\; ^{2\; {k_{z}{({Q/2})}}z_{0}}{\overset{\sim}{\overset{\sim}{S}}\left( {Q,k} \right)}^{{- }\; k\; t_{0}}}_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}}} & (71) \\ {{{\overset{\sim}{\overset{\sim}{\eta}}}^{+}\left( {Q,\beta} \right)} = {{{\overset{\sim}{\overset{\sim}{B}}\left( {Q,k} \right)}i\; ^{{\{{{2{k_{z}{({Q/2})}}z_{0}} - {kt}_{0}})}}{\overset{\sim}{\overset{\sim}{S}}\left( {Q,k} \right)}}_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}}} & (72) \end{matrix}$

This equation may be simplified by having the relative time offset t₀ and the focus offset z₀ coincide at t₀=0 and z₀=0.

FIG. 30 shows a data flow diagram for the prototype ISAM algorithm for 2D imaging where in the paraxial limit ill now describes a single transverse dimension. It is noted that the other transverse dimension may be solved separately in so much as the paraxial approximation holds. The prototype algorithm was designed in Matlab, a mathematical software package, where all the calculations were done in double precision, 64-bit. The digitized spectra Srω is a function of the M discrete positions r in the plane perpendicular to the beam axis and the N discrete frequencies ω. A non-uniform interpolation is needed to map the sampled frequencies ω to the sampled wavenumbers k. Similarly, the ISAM solution requires a non-uniform interpolation mapping wavenumbers k to longitudinal frequency coordinates of the object β. The cubic B-spline is chosen as the non-uniform resampling interpolator; although, a windowed sinc interpolator, such as the prolate-spheroidal interpolator, may be chosen to select specific convergence characteristics. Unfortunately, the frequency response for many non-uniform interpolation procedures drops in performance for frequencies higher than half the Nyquist rate. To mitigate this effect, each spectrum is interpolated by performing a fast Fourier transform (FFT), padding with N zeros, and performing an inverse FFT (IFFT). The interpolated spectra are stored in a buffer with 2N rows and M columns. Thus, the new interpolated, digitized spectra Srω′ is a function of the sampled positions r and the new sampled frequencies ω′. Similarly, Srk is interpolated by a factor of 2 to get Srk′ as a function of r and the new uniformly sampled wavenumbers k′.

The non-uniformly sampled spectrum in spectral-domain OCT can be corrected in a fashion similar to material dispersion correction by resampling the Fourier spectrum from ω′ to k. A desired reindexing array in is based primarily on calibrated, second- and third-order correction factors α₂ and α₃, respectively.

$\begin{matrix} {{i_{n} = {{2n} + {\alpha_{2}\left( {\frac{2n}{N} - \omega_{ctr}} \right)}^{2} + {\alpha_{3}\left( {\frac{2n}{N} - \omega_{ctr}} \right)}^{3}}},} & (73) \end{matrix}$

where n is an integer between 0 and N−1, 2N is the number of samples of the interpolated spectrum S_(rω), and ω_(ctr) is the calculated centroid of the spectrum on a scale from 0 to 1. α₂ and α₃ are set through a calibration routine. A mirror models a perfect reflector with a minimized width of the point spread function (PSF). Thus, α₂ and α₃ are adjusted such that the imaged PSF is indeed minimized.

FIG. 30 shows a data flow chart of the prototype algorithm which has been broken down into the eight steps listed below.

Step 1 The spline coefficients and interpolations are computed as described above. The result is stored in an array S_(rk′) where k′ is the uniformly sampled wavenumber. Step 2 The 1-D FFT of the columns of S_(rK′) is taken to get the signal S_(rt) where t is the sampled time delay of the optical signal. The Hermitian symmetric values, where t<0, are removed. There will be no ambiguity, if the reference arm is placed such that the reference light pulse arrives at the spectrometer before the sample light pulses. The complex analytic OCT signal is represented by S_(rt). Step 3 A phase correction procedure is implemented to ensure phase stability for the ISAM reconstruction. A glass coverslip can be placed on top of the sample to track and reduce system instabilities. The phase corrected signal is represented as Ŝ_(rt). Step 4 The contribution of the constant spectral intensity is removed by setting Ŝ_(rt) to zero, for values near t=0. Then, a coordinate change from t to t′ is made by circularly shifting the rows such that the focal plane lies at t′=0, which coincides with z′=0 where the solution is derived in equation (72). The data Ŝ_(rt′) is padded with 2|t₀| rows of zeros to prevent aliasing of the shifted data, where t₀ is the number of time delay samples from the focus to the center of Ŝ_(rt). Step 5 The 2-D IFFT of Ŝ_(rt′) is taken to get S_(qk). Step 6 The 2-D ISAM resampling grid, spline coefficients, and the interpolations are calculated. Then the result is multiplied by {tilde over ({tilde over (B)}(Q,k)e^(iπ/2) to get η_(qβ). Step 7 The 2-D FFT of η_(qβ) is taken to get η_(rz′), where z′=0 at the focal plane. Step 8 A coordinate change from z′ to z is made by circularly shifting the rows such that the reference delay lies at the top of the image and corresponds to the z=0 plane. Then, the magnitude of the ISAM reconstruction η_(rz) is calculated resulting in ISAM amplitude image |η_(rz)|.

There are a number of operations hindering the performance of the prototype ISAM algorithm. Using C++ instead of Matlab allows for a number of speed improvements. The 64-bit operations such as the FFT and interpolations can be replaced with 32-bit operations with a small, but tolerable, increase of quantization noise. A speed advantage is gained by replacing the ‘for’ loops within Matlab scripts by vectorized Intel SSE (Streaming SIMD Extentions) commands and/or compiled ‘for’ loops. Time-expensive, built-in Matlab interpolation and FFT functions are replaced with hardware optimized functions as found in the Intel Math Kernel Library (MKL). An FFT of the real spectrum is implemented using the customized real-to-complex FFT in the MKL. The resampling step corrects the depth dependent defocus and is crucial for the performance of the algorithm. Although, the filter in equation (72), B(Q,k)e^(iπ/2), can be highly singular which introduces noise, hence the need for regularization. Furthermore, applying the filter provides a quantitative, but not a significant qualitative change to the data. Thus, equation (72) is reduced to an unfiltered solution

$\begin{matrix} {{{\overset{\sim}{\overset{\sim}{\eta}}}^{+ ''}\left( {Q,\beta} \right)} = {{\overset{\sim}{\overset{\sim}{S}}\left( {Q,k} \right)}_{k = {\frac{1}{2}\sqrt{\beta^{2} + Q^{2}}}}}} & (74) \end{matrix}$

without degradation of the Fourier space resampling. The focal plane is fixed such that t₀=0 by imposing a restriction that the focus be placed at the center of the image. Therefore, the complex analytic signal does not need to be padded with any zeros, and thus the computation time of the FFT is reduced because the FFT is always a power of two. While the prototype functions utilized dynamically allocated memory, the real-time program allocates memory prior to imaging time. Similarly, a table of resampling coefficients for the dispersion compensation and the ISAM reconstruction are pre-calculated and stored in memory. The prototype algorithm interpolated the data by two to mitigate the high frequency roll-off of the non-uniform interpolator. Although the interpolation has good frequency response, it is not necessary, especially when speed is an issue. The phase stabilization procedures, which might be needed for long acquisition periods, are not necessary for 2-D imaging since this SD-OCT system provides good phase stability over the short duration of the scan, about 17 ms.

The key computation for ISAM is the resampling in the Fourier space. The new design is an efficient routine which requires two interpolations of the columns, one one-dimensional (1 D) real-to-complex (R2C) fast Fourier transform (FFT) of the columns, and two 2D FFTs. The FFT routine from the Intel Math Kernel Library (MKL) was used for all 1D and 2D transforms. The 1D 2048-point R2C FFT is calculated for every column of the 512×2048 real-valued data, while the 2D FFT and 2D IFFT are calculated for the 512×1024 complex values.

The reindexing array in and the corresponding cubic B-spline interpolation table is pre-computed and stored in random access memory (RAM) for repeated use. The coefficients for the cubic B-spline are pre-computed. The integer part of the index used for calculation of the in the cubic B-spline is given by

$\begin{matrix} {{a_{x}\lbrack n\rbrack} = \left\{ {\begin{matrix} {{\left\lfloor i_{n} \right\rfloor + x},} & {0 \leq {\left\lfloor i_{n} \right\rfloor + x} \leq {N - 1}} \\ {0,} & {{\left\lfloor i_{n} \right\rfloor + x} < 0} \\ {N - 1} & {{\left\lfloor i_{n} \right\rfloor + x} > {N - 1}} \end{matrix},{x = {- 1}},0,1,{{2\mspace{14mu} {and}\mspace{14mu} 0} \leq n < N}} \right.} & (75) \end{matrix}$

The fractional coefficients are given by

f _(n) =i _(n) −└i _(n)┘, 0≦n<N  (76)

and

$\begin{matrix} {\begin{matrix} {{b_{- 1}\lbrack n\rbrack} = {\left( {1 - f_{n}} \right)^{3}/6}} \\ {{b_{0}\lbrack n\rbrack} = {\left( {4 - {6f_{n}^{2}} + {3f_{n}^{3}}} \right)/6}} \\ {{b_{1}\lbrack n\rbrack} = {\left( {1 + {3f_{n}} + {3f_{n}^{2}} - {3f_{n}^{3}}} \right)/6}} \\ {{b_{2}\lbrack n\rbrack} = {f_{n}^{3}/6}} \end{matrix},{0 \leq n < N}} & (77) \end{matrix}$

Next, the Fourier resampling indices of ISAM are pre-calculated. The constants which specify the axial and transverse bandwidths of the object, based on system parameters, are βmin, βmax, qmin, and qmax, respectively. These constants are selected in accordance to the specific bandwidth parameters of the system and describe the boundaries of the Fourier space shown in FIG. 29( c). By defining the longitudinal bandwidth parameters of the object rather than the wavenumber, we can avoid computationally costly zeropadding of the resampled solution. However, a small loss of spectral information across the β_(min) boundary may reduce the signal-to-noise ratio, but only marginally. In this case, β_(min) and β_(max) are set to be the boundaries of the optical bandwidth, q_(min) is set to zero, and q_(max) is set to the maximum transverse scanning frequency. More important than the exact values for β_(min), a β_(max), q_(min), and q_(max), is the ratio of the corresponding transverse and longitudinal bandwidths. The maximum and minimum wavenumber are calculated for the region of interest,

k _(min)=β_(min)/2  (78)

k _(max)=0.5√{square root over (β_(max) ² +q _(max) ²)}.  (79)

A range of values for q[m] and β[n] is created in the 2-D Fourier space and the resampling grid kq[m,n] is pre-calculated. Notice here that M and N′=N/2 are assigned according to number of rows and columns in the complex analytic sampled Fourier data.

$\begin{matrix} {{q\lbrack m\rbrack} = \left\{ {\begin{matrix} {{m\; \frac{2q_{\max}}{M}},} & {0 < m \leq {M/2}} \\ {{\left( {m - M} \right)\frac{2q_{\max}}{M}},} & {{M/2} < m \leq M} \end{matrix},} \right.} & (80) \\ {{{\beta \lbrack n\rbrack} = {{{n\left( {\beta_{\max} - \beta_{\min}} \right)}/N^{\prime}} + \beta_{\min}}},{0 \leq n < N^{\prime}},} & (81) \\ {{{{kq}\left\lbrack {m,n} \right\rbrack} = {{\frac{N^{\prime}}{k_{\max} - k_{\min}}\left( {{0.5\sqrt{{\beta \lbrack n\rbrack}^{2} + {q\lbrack m\rbrack}^{2}}} - k_{\min}} \right)} + 1}},{0 \leq n < N^{\prime}},{0 \leq m < M}} & (82) \end{matrix}$

The kq[m,n] grid is used to calculate a table of values for the cubic B-spline coefficients. The values are calculated as shown above except each column of resampling parameters is different and therefore must also be saved. FIG. 29( b) shows the plot of the kq[m,n] grid where the curved lines represent the constant values of β[n]. This 2D grid is used to calculate another table of cubic B-spline coefficients. The spline values are calculated as shown above except each column of the resampling parameters is different and therefore 2D spline coefficients are stored in memory.

Similar to the spline coefficient calculations shown above, the reindexing array kq[m,n] and the corresponding cubic B-spline interpolation coefficient table is pre-computed and stored in random access memory (RAM) for repeated use. The integer part of the index used for calculation of the in the cubic B-spline is given by

$\begin{matrix} {{a_{q,x}^{\prime}\left\lbrack {m,n} \right\rbrack} = \left\{ {{{\begin{matrix} {{\left\lfloor {{kq}\left\lbrack {m,n} \right\rbrack} \right\rfloor + x},} & {0 \leq {\left\lfloor {{kq}\left\lbrack {m,n} \right\rbrack} \right\rfloor + x} \leq {N^{\prime} - 1}} & \; \\ {0,} & {{\left\lfloor {{kq}\left\lbrack {m,n} \right\rbrack} \right\rfloor + x} < 0} & {{;{x = {- 1}}},0,1,{2;}} \\ {{N^{\prime} - 1},} & {{\left\lfloor {{kq}\left\lbrack {m,n} \right\rbrack} \right\rfloor + x} > {N^{\prime} - 1}} & \; \end{matrix}\mspace{79mu} 0} \leq n < N^{\prime}};{0 \leq m < M}} \right.} & (83) \end{matrix}$

The fractional coefficients are given by

f _(m,n) =kq[m,n]−└kq[m,n]┘, 0≦n<N′; 0≦m<M  (84)

and

$\begin{matrix} {{{b_{q,{- 1}}^{\prime}\left\lbrack {m,n} \right\rbrack} = {\left( {1 - f_{m,n}} \right)^{3}/6}}{{b_{q,0}^{\prime}\left\lbrack {m,n} \right\rbrack} = {\left( {4 - {6f_{m,n}^{2}} + {3f_{m,n}^{3}}} \right)/6}}{{b_{q,1}^{\prime}\left\lbrack {m,n} \right\rbrack} = {\left( {1 + {3f_{m,n}} + {3f_{m,n}^{2}} - {3f_{m,n}^{3}}} \right)/6}}{{{b_{q,2}^{\prime}\left\lbrack {m,n} \right\rbrack} = {f_{m,n}^{3}/6}},{{0 \leq n < N^{\prime}};{0 \leq m < M}}}} & (85) \end{matrix}$

Using the pre-calculated tables, a flow diagram of the real-time algorithm is shown in FIG. 31.

Here S_(rω)[m,n] is the raw interferometric data captured from the camera and has M columns and N rows. In this implementation, M=512 columns and N=2048 rows.

Step 1 The pre-calculated table is used to perform the interpolation as follows.

S _(rk) [m,n]=S _(rω) [m,a ₋₁ {n}]b ₋₁ {n}+S _(rω) [m,a ₀ {n}]b ₀ {n}+S _(rω) [m,a ₁ {n}]b ₁ {n}+S _(rω) [m,a ₂ {n}]b ₂ {n},  (86)

for all integers 0≦n<N and 0≦m<M. Step 2 The real-to-complex 1-D FFT routine from the Intel Math Kernel Library (MKL) is used on all the columns.

$\begin{matrix} {{{S_{rt}\left\lbrack {m,n} \right\rbrack} = {\sum\limits_{k = 0}^{N - 1}{{S_{rk}\left\lbrack {m,k} \right\rbrack}^{{- \frac{2{\pi }}{N}}{kn}}}}},{0 \leq n < {N\mspace{14mu} {and}\mspace{14mu} 0} \leq m < M}} & (87) \end{matrix}$

The real-to-complex FFT will compute N/2 complex values. The new number of rows of the complex data is given by N′=N/2. Step 3 The contribution of the noise from the average spectral intensity on the detector is removed by setting S_(rt)[m,n] equal to zero at the t=0 plane. Also, S_(rt)[m,n] is circularly shifted by half such that the focus will be the new t′=0 plane.

$\begin{matrix} {{S_{{rt}^{\prime}}\left\lbrack {m,n} \right\rbrack} = \left\{ {{\begin{matrix} {S_{rt}\left\lbrack {m,{n + {N^{\prime}\text{/}2}}} \right.} & {0 \leq n < {N^{\prime}\text{/}2}} \\ 0 & {{N^{\prime}\text{/}2} \leq n < {{N^{\prime}\text{/}2} + 2}} \\ {S_{rt}\left\lbrack {m,{n - {N^{\prime}\text{/}2}}} \right\rbrack} & {{{N^{\prime}\text{/}2} + 2} \leq n < N^{\prime}} \end{matrix}{and}\mspace{14mu} 0} \leq m < {M.}} \right.} & (88) \end{matrix}$

Step 4 The complex 2-D inverse FFT (IFFT) of the complex analytic signal S_(rt′)[m,n] is calculated

$\begin{matrix} {{{S_{qk}\left\lbrack {m,n} \right\rbrack} = {\frac{1}{M\; N^{\prime}}{\sum\limits_{r = 0}^{M - 1}{\sum\limits_{t = 0}^{N^{\prime} - 1}{{S_{{rt}^{\prime}}\left\lbrack {r,t} \right\rbrack}^{\frac{2{\pi }}{N^{\prime}}n\; t}^{\frac{2\pi \; }{M}{mr}}}}}}},{0 \leq n < {N^{\prime}\mspace{14mu} {and}\mspace{14mu} 0} \leq m < {M.}}} & (89) \end{matrix}$

Step 5 The pre-calculated table is used to perform the cubic B-spline interpolation as follows.

η_(qβ) [m,n]=S _(qk) [m,a _(q,-1) ′{m,n}]b _(q,-1) ′{m,n}+S _(qk) [m,a _(q,0) ′{m,n}]b _(q,0) ′{m,n}+S _(qk) [m,a _(q,1) ′{m,n}]b _(q,1′) {m,n}+S _(qk) [m,a _(q,2) ′{m,n}]b _(q,2) ′{m,n}, 0≦n<N′ and 0≦m<M,  (90)

where the calculated cubic B-spline coefficients are from the lookup table. Step 6 The complex 2-D FFT of the Fourier transformed object η_(qβ)[m,n] is calculated

$\begin{matrix} {{{\eta_{{rz}^{\prime}}\left\lbrack {m,n} \right\rbrack} = {\sum\limits_{q = 0}^{M - 1}{\sum\limits_{\beta = 0}^{N^{\prime} - 1}{{\eta_{q\; \beta}\left\lbrack {q,\beta} \right\rbrack}^{{- \frac{2{\pi }}{N^{\prime}}}\beta \; n}^{{- \frac{2{\pi }}{M}}{qm}}}}}},{0 \leq n < {N^{\prime}\mspace{14mu} {and}\mspace{14mu} 0} \leq m < {M.}}} & (91) \end{matrix}$

Step 7 η_(rz′)[m,n] is circularly shifted such that the focus is in the middle of the image,

$\begin{matrix} {{\eta_{rz}\left\lbrack {m,n} \right\rbrack} = \left\{ {\begin{matrix} {\eta_{{rz}^{\prime}}\left\lbrack {m,{n + {N^{\prime}\text{/}2}}} \right\rbrack} & {0 \leq n < {N^{\prime}\text{/}2}} \\ {\eta_{{rz}^{\prime}}\left\lbrack {m,{n - {N^{\prime}\text{/}2}}} \right\rbrack} & {{N^{\prime}\text{/}2} \leq n < N^{\prime}} \end{matrix},} \right.} & (92) \end{matrix}$

then the magnitude |η_(rz)[m,n]| is displayed.

In various embodiments of the present invention, the disclosed methods determining the three-dimensional susceptibility of a sample may be implemented as a computer program product for use with a computer system. Such implementations may include a series of computer instructions fixed either on a tangible medium, such as a computer readable medium (e.g., a diskette, CD-ROM, ROM, or fixed disk) or transmittable to a computer system, via a modem or other interface device, such as a communications adapter connected to a network over a medium. The medium may be either a tangible medium (e.g., optical or analog communications lines) or a medium implemented with wireless techniques (e.g., microwave, infrared or other transmission techniques). The series of computer instructions embodies all or part of the functionality previously described herein with respect to the system. Those skilled in the art should appreciate that such computer instructions can be written in a number of programming languages for use with many computer architectures or operating systems. Furthermore, such instructions may be stored in any memory device, such as semiconductor, magnetic, optical or other memory devices, and may be transmitted using any communications technology, such as optical, infrared, microwave, or other transmission technologies. It is expected that such a computer program product may be distributed as a removable medium with accompanying printed or electronic documentation (e.g., shrink wrapped software), preloaded with a computer system (e.g., on system ROM or fixed disk), or distributed from a server or electronic bulletin board over the network (e.g., the Internet or World Wide Web). Of course, some embodiments of the invention may be implemented as a combination of both software (e.g., a computer program product) and hardware. Still other embodiments of the invention are implemented as entirely hardware, or entirely software (e.g., a computer program product).

While various embodiments of the invention have been described, it will be apparent to those of ordinary skill in the art that other embodiments and implementations are possible within the scope of the invention. Accordingly, the invention is not to be restricted except in light of the attached claims and their equivalents. 

1-29. (canceled)
 30. A system for real-time imaging of tissue, the system comprising: a. a core imaging unit for providing low-coherence optical radiation and coupling said low-coherence optical radiation to any one of an interchangeable set of sample assemblies and for generating OCT data based on combination with a reference beam of scattered light received from said one of the interchangeable set of sample assemblies; b. a sampling device including one of the plurality of sample assemblies, the sampling device adapted to receive the low-coherence optical radiation from the core imaging unit; to illuminate therewith the tissue; and to collect light scattered by the tissue and to return said light to the core imaging unit; and c. a core software unit adapted to receive the OCT data from the core imaging unit; and to provide real-time feedback to a user based on the OCT data.
 31. The system of claim 30, wherein the sampling device is chosen from among handheld sample assemblies, free-space optical devices, and fiber-based devices.
 32. The system of claim 30, wherein the core software unit includes an image classifier.
 33. The system of claim 30, wherein the core software unit is adapted to classify images on the basis of an optical property derived from the OCT data.
 34. The system of claim 33, wherein the optical property is chosen from the group of optical properties including a refractive index, a scattering profile, a scattering coefficient, an anisotropy factor, birefringence, spectral shift, texture, Doppler shifts, phase resolution, phase-resolved Doppler measurements, phase-resolved spectroscopic measurements, light scattering parameters, and spectroscopic absorption.
 35. The system of claim 30, wherein providing real-time feedback to the user includes providing images of the tissue to the user in real time.
 36. The system of claim 35, further comprising a display for displaying images of the tissue to the user.
 37. The system of claim 30, wherein providing real-time feedback to the user includes illuminating an LED.
 38. The system of claim 30, wherein providing real-time feedback to the user includes providing tactile feedback.
 39. The system of claim 30, wherein providing real-time feedback to the user includes providing auditory feedback.
 40. The system of claim 30, wherein the core software unit is further adapted to implement interferometric synthetic aperture microscopy.
 41. The system of claim 30, wherein the core software unit is further adapted to correct for aberrations due to the low-coherence optical radiation.
 42. The system of claim 30, wherein the sampling device is adapted for azimuthal scanning about an axis of an optical fiber.
 43. A system for real-time imaging of tissue, the system comprising: a. a sampling device adapted to receive low-coherence optical radiation; to illuminate the tissue with the low-coherence optical radiation; and to collect light scattered by the tissue; b. a core imaging unit adapted to generate said low-coherence optical radiation and to couple said low-coherence optical radiation to said sampling device and to generate OCT data based on combination scattered light received from the sampling device with a reference beam; and c. a core software unit adapted to receive the OCT data from the core imaging unit; and to provide images of the tissue to a user in real time based on the OCT data.
 44. The system of claim 43, wherein the sampling device comprises: a. a catheter having a tip; and b. a transparent balloon coupled to the tip of the catheter; wherein the sampling device is adapted to illuminate the tissue with the low-coherence optical radiation though the transparent balloon.
 45. A system for real-time imaging of tissue, the system comprising: a. a core imaging unit adapted to generate low-coherence optical radiation; b. a sampling device in communication with the core imaging unit, adapted to receive the low-coherence optical radiation from the core imaging unit and to send a signal back to the core imaging unit, wherein OCT data is generated by the core imaging unit; and c. a core software unit adapted to receive the OCT data from the core imaging unit, to perform further data analysis, and to provide feedback of the OCT data in real time.
 46. The system of claim 45, wherein the further data analysis includes enhancing an image.
 47. The system of claim 45, wherein imaged tissue imaged is classified by running the OCT data though classification algorithms.
 48. The system of claim 47, wherein the classification algorithms analyze the OCT data and classify the tissue imaged using an optical property which is derived from the OCT data.
 49. The system of claim 48, wherein the optical property is chosen from the group of optical properties including a refractive index, a scattering profile, a scattering coefficient, an anisotropy factor, birefringence, spectral shift, texture, Doppler shifts, phase resolution, phase-resolved Doppler measurements, phase-resolved spectroscopic measurements, light scattering parameters, and spectroscopic absorption. 